alloying elements of magnesium alloys a literature review

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Home > Books > Magnesium Alloys Structure and Properties

Alloying Elements of Magnesium Alloys: A Literature Review

Submitted: 12 December 2020 Reviewed: 26 January 2021 Published: 17 February 2021

DOI: 10.5772/intechopen.96232

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Magnesium alloys are the lightest structural metal. The lightness is the main reason for the interest for Mg in various industrial and clinical applications, in which lightweight structures are in high demand. Recent research and developments on magnesium Mg alloys are reviewed. A particular attention is focused on binary and ternary Mg alloys consisting mainly of Al, Zn, Mn, Ca and rare earth (RE) elements. The effects of different alloying elements on the microstructure, the mechanical and the corrosion properties of Mg alloys are described. Alloying induces modifications of the microstructural characteristics leading to strengthening mechanisms, improving then the ductility and the mechanical properties of pure Mg.

• magnesium alloy
• alloying element
• strengthening
• mechanical properties

Author Information

Nouha loukil *.

• Laboratory of Materials Engineering and Environment, Sfax, Tunisia

*Address all correspondence to: [email protected]

1. Introduction

Magnesium alloys are the lightest structural metal view to the very low density of 1.74 g/cm 3 and designed as Green Structure Metal [ 1 ]. Taking into account its very negative potential (−2.34 V), Mg is a reducing agent and is able to combine with oxygen, sulfur and halogen compounds. This reducing power finds its interest in the production of sacrificial anodes that prevents corrosion. Meanwhile, this reducing agent constitutes a major barrier to the use of Mg as a structural material. In addition to this undesirable property, poor wear resistance of pure Mg hinders its use for different applications.

That’s why, pure Mg is combined with other metal elements to improve their properties even at high temperatures, namely manganese, aluminum, zinc, silicon, copper, zirconium and rare-earth metals. Mg alloys, non-ferrous material, are characterized with low density, high ductility, strength and acceptable corrosion resistance.

The lightness is the main reason for the interest in the civil and military transport sector for Mg, in which lightweight structures are required. When compared with metallic structure namely, aluminum Al and iron Fe, the density of Mg is much lower than those of these metals [ 2 ]. In reverse, Mg exhibits similar specific mechanical properties, mainly excellent castability and machinability compared to a metal which is durable [ 3 , 4 ]. When used as alloying element in metallic material, Mg enhances the mechanical properties of Aluminum and the malleability of the iron.

Compared to that of metallic structures, Mg alloys show higher weight/strength ratio. They possess an elastic modulus of 45 GPa and tensile strength of 160–365 MPa [ 5 ]. Based on the above reasons, Mg alloys have been widely used in the aerospace industry, mechanic manufacture and automotive industry. Indeed, the replacement in the three major components (body, power train and chassis) of a vehicle by Mg alloys lead to weight reduction of 20–70% [ 6 ].

Mg alloys provides an excellent property of damping vibration and heat dissipation property which is an important factor for different automobile and aerospace industries. As well known, the vibration is a kind of loss and affects the efficiency of the vehicle.

Special attention is paid to Mg-based materials for clinical applications (orthopedic applications, critical wounds …) owing to its density that is very close to that of human bone (1.75 g/cm 3 ), higher specific strength and low elastic modulus. Furthermore, Mg is biocompatible as it is essential for several biological reactions and as a co-factor for enzymes.

Quite opposite to the conventionally used metallic materials such as stainless steel and Ti alloys that exhibit stress shielding and metal ion releases, Mg is biodegradable. That is to say, Mg entirely degrades in the human body preventing then the need for second surgical procedure to remove the implants material [ 7 ]. This has received a widespread attention from the scientific and medical community [ 8 ]. However, the biodegradability of implanted Mg alloys is hindered by an accelerated degradation rate in chloride-abundant environments like human body [ 9 ]. Generally, the period of bone remodeling is about 3 to 6 months. To be wary of this suggestion, the rate of degradation must be controlled by suitable surface modification in order to enhance the duration of effectiveness of the implantable material.

Researchers have been working on synthesis and characterization of Mg-based biomaterials with a variety of composition in order to control the degradation rate of Mg that leads to a loss of mechanical properties and contamination in the body. The alloying elements affect the characteristics and performance of Mg alloys.

This paper is a comprehensive review that compiles the recent literature on the important alloying elements and their impacts on the properties of Mg alloys.

2. Designation and types of Mg alloys

According to the addition elements, Mg alloys are designated in different ways. Alloys are designated by letters corresponding to their main addition elements followed respectively by the percentage of each element. The American Society for Testing and Materials ASTM developed a method to designate Mg alloys which are named by their main alloying elements. The first two letters indicate the alloying elements used in the greatest quantity. One or two letters are followed by numbers which represent the percentage by weight of the elements rounded to the nearest whole number. The ASTM code for alloying elements is as follows, aluminum is designated by the letter A, zinc by the letter Z, manganese by the letter M, silicon by the letter S, yttrium by the letter W, zirconium by the letter K, silver by the letter Q, thorium by the letter H. The most common families are: AZ (example AZ31), AM (example AM60), AS (example AS41), WE (example WE43) and AE (example AE42). For instance, AZ91 Mg alloy contains 9% of Al and 1% of Zn and the rest by pure Mg.

Based on the process of operation, Mg alloys can be categorized into two groups: cast alloys and wrought alloys.

2.1 Cast Mg alloys

Cast alloys are basically made by pouring the molten liquid metal into a mold, within which it solidifies into the required shape. Depending on the chemical composition, there are two groups of cast Mg alloys [ 10 ].

The first group includes Mg-Al alloys in which Al amount does not exceed 10% with an addition of Zn and Mn. These alloys are characterized by a low cost of manufacture. Indeed, this criterion is recommended for the industrialization and the commercialization of high performance of Mg alloys. The most commonly used is AM50 alloy mainly for die casting, and AZ91 for sand and die casting method. Meanwhile, their disadvantage is a low operating temperature-below 120 °C. The aging hardenability of these Mg-Al based alloys, such as AM60 alloy, is relatively poor. That’s why, these alloys are prepared by high pressure die casting with relatively high cooling rate. The strength, the castability, the workability, the corrosion resistance and the weldability of these commercial AZ91 and AM60 alloys are not satisfying, but can be improved by introducing alloying elements. For instance, AZ91 alloy’s strength is relatively high; however, its ductility is not so good due to the high Al content. Whereas, AM60 alloy has high ductility, but its strength is relatively low. Various alloying elements such as Ce, Nd, Y, Si, Ca, Ti, B, Sr., Sb, Bi, Pr have been used to enhance the operating temperature and the mechanical properties of modified AZ91 alloy [ 11 ]. Among these alloying elements Ce, Nd, Y, Bi and Sb are effective to improve the tensile properties of AZ91 alloy. For the modified AM60 alloys, various alloying elements, Ti, Nd, Sn and Ce elements are relatively effective to further enhance the mechanical properties of AM60 alloy. For instance, the tensile strength of 280 MPa and elongation of 11% could be obtained [ 12 ].

The second group of alloys is free from Al, but containing mostly Zn, rhenium RE and Y with an addition of Zr. Such alloys are recommended for high temperature until 250 °C, but the cost of their production increases due to the cost of alloy additions. The common commercial WE43 and WE54 alloys can be cast by sand casting process with a low cooling rate. Accordingly, the mechanical properties are further improved by solution and aging treatment. These alloys are largely used as sand castings. The strength of WE54 is basically attained via precipitation strengthening. Depending on the aging temperature and time, the precipitating sequence in WE alloys has been reported to involve the formation of phases β″, β′, and β. The equilibrium β phase is isomorphic to the Mg 5 Gd phase and is identified as a Mg 14 Nd 2 Y phase [ 13 ].

The mechanical properties of the cast alloys are determined on poured test bars according to standard ASTM procedures.

2.2 Wrought alloys

Wrought alloys are destined to mechanical working, such as forging, extrusion and rolling operations to shaping. Al, Mn and Zn are also the main alloying elements. Wrought alloys of Mg are sorted into heat treatable and non-heat treatable alloys. The use of wrought Mg alloys is limited less than 10%. This is due to the poor cold workability of the hexagonal close packed (HCP) crystal structure of Mg, generating low formability at room temperature. New Mg alloys have been developed to enhance their strength by modifying the existing alloy [ 14 ] or by grain refinement. It was also reported that advanced processing, such as hot extrusion, rolling, forging are able to refine the microstructure and improve the mechanical properties of Mg alloys. Many commercial wrought Mg alloys have been developed, such as AZ system, ZK system… Compared with wrought Mg alloys, casting Mg alloys have economical advantages due to their shorter processing cycle. Therefore, casting Mg alloys obtain more incremental use of almost 90% of total application products.

Based on literature data, new Mg alloys with high strength can be developed when modified the present commercial cast and wrought alloys [ 15 ] by strengthening mechanisms: alloying, grain refinement, precipitation and texture strengthening effect. To overcome the weakness of pure Mg, different elements have to be alloying with pure Mg to obtain Mg alloys with desired mechanical properties. Mg alloys shows an excellent specific strength and stiffness with dimensional stability due to its hexagonal crystal structure and to its atomic size (about 320 nm). Much progress has been achieved in strengthening of Mg alloys through solid solution strengthening using different alloying elements. The effects of such elements on the microstructure and mechanical properties are described.

2.2.1 Aluminum

Mg alloys including Al are called Mg-Al binary alloys. Al is the most widely used alloying element of Mg alloys as structural materials [ 16 ]. Indeed, Al improves the tensile strength, the ductility and the castability of Mg alloys at temperature not exceeding 120 °C [ 17 ]. If the amount of Al varies from 1 to 9%, the grains size of Mg-Al alloys decreases, increasing accordingly the micro-hardness [ 18 ]. Zheng et al. [ 18 ] demonstrated that the average grain size of Mg-Al alloy falls from 3097 μm to 111 μm if Al amount increases from 1% to 9%. Figure 1 shows the influence of the addition of Al on the size of α-Mg dendrites for Mg-Al binary alloys. It can be seen that with 1% of Al to pure the structure of Mg, α-Mg dendrites are transformed from columnar to equiaxial ( Figure 1 ). With higher Al amount, α-Mg dendrites become more developed and the dendrite arms become finer [ 18 ]. According to Mg-Al binary alloy phase diagram [ 19 ], α-Mg dendrite firstly precipitates during the solidification process, and then expels the redundant Al solute. In fact, this precipitation releases latent heat, causing an increase of the melt temperature ahead of the solidification interface. It decreases the degree of super-cooling, and suppresses the growth of α-Mg dendrites, leading to the grain refinement [ 18 ]. When Al exceeds 2%, an eutectic microstructure involving α-Mg and Mg 17 Al l2 will be formed along the grain boundaries. The Mg 17 Al 12 phase improves the corrosion potential and reduces the corrosion rate [ 20 ]. However, the Mg 17 Al 12 phase has a relatively low melting temperature (437 °C), giving arise to the microstructure instability over 120 °C. This occurrence related to the grain boundary sliding explains the degradation of the mechanical properties of Mg-Al alloys at elevated temperatures [ 21 ]. Moreover, the micro-hardness of the α-Mg matrix increases from 36.3 HV to 50.1 HV. This increase is recognized to solution strengthening caused by Al solubilized in the α-Mg matrix.

Size and morphology of α-Mg dendrites of Mg-Al binary alloys with various Al amount [ 18 ].

The most popular alloys are Mg-Al-Zn (AZ) and Mg-Al-Mn (AM) as Zn improves the ambient temperature mechanical properties and Mn enhances the creep resistance of alloys [ 22 ].

2.2.2 Zinc Zn

Zinc is added in Mg alloys to enhance the tensile properties. Zinc decreases the weldability property [ 23 ]. Above 1% of Zn, it provides strengthening to Mg by solid solution [ 24 ]. If zinc is added in higher amount, the Mg alloy presents hot cracking and lower ductility [ 23 ]. In addition, micro porosity of sand casted Mg alloys is observed with an Al amount ranging from 2% to 10%. The dissolution of Zn in Mg diminishes its reducing power, improving then its oxidation resistance [ 25 ]. The corrosion rate of Mg-Zn alloys decreases with increasing Zn in Mg matrix. For instance, the corrosion rate of Mg-3%Zn alloy is 34.6% lower than that of pure Mg compact. Zhang et al. [ 26 ] reported that 6% of Zn diminishes the corrosion rate of the Mg alloy for implant applications.

The micro structural analysis indicates smaller grain size at higher Zn content. The reason for the grain sizes refinement is recognized to close-packed hexagonal structure of both Mg and Zn metals. The diffusion rate of Zn atoms in Mg matrix is fast, favoring an easier diffusion into Mg matrix and forming Mg solid solution or intermetallic compounds. Figure 2 shows surface scanning micrographs of Mg-Zn alloys with various Zn content. The phases present in Mg-Zn alloys depend on the Zn amount. Figure 2 shows some white phase along the Mg grain boundary. This white phase increases with higher Zn content, hindering both the movement of the grain boundary and the grain growth [ 27 ]. For instance, Mg-3%Zn alloy is mainly composed of α-Mg phase, whereas Mg-4%Zn alloy is composed of α-Mg and MgZn 2 phases [ 27 ]. The micro-hardness for different Mg-Zn alloys continuously increases with increasing Zn content. For illustration, the micro-hardness HV of Mg-3%Zn alloy is about 45% higher than those of pure Mg samples.

SEM images of Mg-Zn alloys with different Zn contents: (a) 1% Zn and (b) 4% Zn [ 27 ].

Mg-Zn based alloys are the most popular wrought Mg alloys with good room temperature strength and ductility. Recent researches attempt to develop new type wrought Mg-Zn alloys using the addition of alloying elements including RE (rare earth), non-toxic Ca, Sn and Mn to optimize the properties of Mg-Zn alloys at room and high temperatures. Mg-Zn-Zr (ZK) is the strongest system owing to good strength and elongation at room temperature.

The use of Mg-Zn alloys in medical applications as bio degradable materials is one of the research areas [ 28 ]. It is well known that the adding element Zn is one of the indispensable trace elements in the human body that promotes the growth, stimulates healing and participates in enzyme synthesis.

2.2.3 Manganese

The alloying element Mn improves the corrosion resistance of Mg alloy and limits the presence of harmful cathodic impurities such as Fe, Ni by the formations of intermetallic compound …. As matter of fact, such impurities lead to galvanizing oxidation of Mg [ 29 ]. Mn combines with impurities in order to moderate the corrosion of Mg-Al alloys. In the presence of Al and Fe, adding Mn produces an intermetallic phase Al 8 (Mn,Fe) 5 that moderate the corrosion rate caused by Fe [ 30 ]. Until now, the exact Mn content addition required to counter-act the detrimental effect of the Fe impurity are still unknown.

With Al, the limit of solubility of Mn in the solid solution of Mg decreases, the strengthening by solid solution induced by Mn remains limited. That’s why, the addition of Mn does not improve the mechanical properties of Mg. When investigated the effect of adding Mn into Mg-Gd alloys, Zhao et al. [ 31 ] demonstrated that the strength of alloys gradually increases while the ductility deteriorates. The main reasons are related to the combination of fine-grained strengthening, precipitation strengthening and texture strengthening [ 31 ]. In this regard, Cho et al. [ 32 ] stated that Mn refines grains of Mg-4Zn-0.5Ca alloy. This occurrence is due to the solute at the S/L interface aggregates in presence of Mn element, resulting different degrees of structural overcooling. Based on the biosafety to the human body, Mn can be accepted by the human body [ 32 ].

Incorporating Ca in Mg alloys can improve the mechanical properties and the corrosion behavior of Mg-Ca alloys. Ca is considered as an alloying element to develop Mg alloys for biomedical applications owing to their good biocompatibility.

As well known, Ca accelerates the bone growth. Moreover, cytocompatibility evaluation results indicated that Mg-1%Ca alloy induces no toxicity to human cells. In this regard, Li et al. [ 33 ] investigated the biodegradability within bone of Mg-Ca alloys with various Ca amounts ranging from from 1 to 20%. It was reported that 20% of Ca content makes Mg alloy very brittle.

Mg-Ca alloys with 0.6–1% Ca were reported to exhibit good mechanical properties and corrosion resistance [ 34 ]. The elongation of Mg-Ca alloy samples decreases with rising Ca content.

Previous studies suggested that Mg-Zn-Ca alloy system is a promising candidate for biodegradable implants in biomedical applications. With the increase of Ca content, the yield strength of Mg-Zn-Ca alloy increases. The addition of Ca to Mg-6%Zn alloy inhibits dynamic recrystallization and grain growth. Microstructural results indicate that Mg-Zn-Ca alloys consist of α-Mg matrix and Ca ₂ Mg ₆ Zn ₃ /Mg ₂ Ca intermetallic phase mainly distributed along grain boundary [ 35 ].

High Ca content improves mechanical properties, while it is detrimental to corrosion resistance due to the micro-galvanic corrosion acceleration [ 36 ]. Literature data revealed that Mg-5%Zn-1%Ca exhibits excellent corrosion resistance and good biocompatibility.

2.2.5 Yttrium Y

Generally, the addition of Yttrium (Y) aims to improve elevated temperature plasticity and the creep resistance of Mg alloys. Wu et al. [ 37 ] studied the mechanical properties of pure Mg and binary Mg-Y alloys. They demonstrated that the elongation is proportional with the Y content, but the strength decreases. Adding Yttrium to Mg-Zn alloys is effective to weaken and change the basal texture of wrought Mg alloys [ 38 ].

When added to the cast alloy ZK60, the mechanical properties and ductility are enhanced at elevated temperature. This is ascribed to the formation of ternary Mg-Zn-Y phase with high thermal stability [ 39 ]. Meanwhile, alloys containing yttrium are expensive.

2.2.6 Rare earths RE elements

The rare Earths elements are common incorporating elements in Mg alloys. A large number of rare-earth elements have been investigated and proven to successfully refine the crystals and to enhance the creep and the corrosion resistance at elevated temperatures required for automobile engineering. Due to their high solubility in Mg, RE elements strengthen Mg alloys either by solid solution strengthening or precipitation hardening mechanisms [ 36 ]. For instance, the addition of RE elements to Mg-Al alloys accelerate the formation of the thermally stable (Mg,Al)xREy phases to improve the high temperature mechanical properties of wrought Mg alloys.

Depending on the chemical composition, various amounts of precipitates can be observed. Figure 3 exhibits small precipitates containing Mg, Zn and O in Mg-1.5Zn ( Figure 3a ), while precipitates in the RE-containing alloys consist of Mg, Zn and RE elements [ 27 ]. The amount of precipitates of Mg-1.5Zn-0.2Gd alloys are more than Mg-1.5Zn alloy, leading to smaller grain size of this alloy. Compared with other rare earth elements, Gd shows higher solubility in Mg, allowing simultaneous solid solution hardening and precipitation strengthening, enhancing then the thermal stability of the microstructure in Mg alloys [ 27 ]. Yang et al. [ 39 ] pointed out that Gd acts as grain refinement and grain boundary strengthening. In this regard, Liu et al. [ 40 ] reported that Mg-1.5Zn-0.2Gd alloy exhibits higher plasticity with the elongation of 27%. Meanwhile, Gd simultaneously reduces the toughness [ 36 ]. These Mg alloy systems containing large amounts of rare-earth for solid solution strengthening result high costs for many practical applications.

Microstructural (SEM) of Precipitates in Mg alloy (a) Mg-1.5%Zn; (b) Mg-1.5%Zn-0.2%Gd [ 27 ].

3. Conclusion

The attractive properties of Mg alloys include light weight, high specific strength, excellent castability and machinability …. However, these alloys have limited formability, limiting their industrial application. Strengthening of Mg alloys via the introduction of solid solution atoms and grain refinement additives are effective approaches. Much progress has been achieved in the development of high strength Mg alloys through solid solution strengthening using various types of solute atoms. Researchers incorporated various alloying elements such as Al, Zn, Ca, Mn and RE elements in Mg matrix. The chemical composition of Mg alloys affects the microstructure and then improves the mechanical properties and corrosion resistance.

The most commercial are the casting magnesium alloys such as AZ91, AM60 and WE43 due to their low cost. Meanwhile, the Mg alloy systems containing rare-earth and noble metal elements for solid solution strengthening result high costs. The heat treatment and the grain refinement via severe plastic deformation methods represent new approach to further strengthening of Mg alloys.

Conflict of interest

The authors declare no conflict of interest.

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REVIEW article

A review on developments in magnesium alloys.

• Department of Metallurgy and Materials Science and Engineering, Faculty of Engineering, Mugla Sitki Kocman University, Muğla, Turkey

In order to facilitate the understanding of the current research efforts and directions, this article first introduces the anomalous/problematic features of magnesium (Mg) and presents the recent approach of stacking fault energy (SFE)–based alloying element selection to lessen or eliminate this problem. Stacking fault energy computations via ab initio techniques necessitate an understanding of the free electron density distribution around atoms in a solid solution. Therefore, the assessment of the role of atoms by also considering the possibility of short range order (SRO) formation rather than a random solid solution has been revisited. Two possible types of SRO have been indicated. The relevant electronic interactions between the host Mg and the alloying element atoms are more clearly incorporated in a generally less known model by Miedema based on atomic-level thermodynamics rather than in Hume–Rothery rules. This more successful approach has also been addressed here. An evaluation founded on these premises, introducing the relatively more recent Mg alloy systems, has been given in terms of their achievements toward healing the problematic features of Mg alloys. The spectrum of alloy systems discussed ranges from doping of Mg to dilute alloy systems and to some rich alloy systems that offer remarkable properties. Among the first category, an unorthodox addition, doping with oxygen, and its implications, has been presented. The dilute alloy systems and their compositional design based on SRO and SFE together with their potentials have been reviewed. Among the rich alloy compositions, the most interesting precipitate systems, that is, the ones involving order and intermetallic formations, long-period stacking order phases, and quasi-crystals, have been discussed. Among all the alloying elements, one that deserves particular attention, calcium, with its implications such as being economical, offering environmentally friendly Mg metallurgy, and remedial effects on the shortcomings of engineering properties, and a closely related issue of calcium oxide (CaO) addition have been scrutinized. This article also makes an attempt to point out the future directions throughout the text, whenever possible.

Introduction

Several complementary reviews to the one presented here can be found in the literature. A very detailed and fascinating history of magnesium (Mg) production and its use have been presented by Witte (2015) . Elegant reviews by Nie (2012) and Pekguleryuz (2013) , covering the spectrum of Mg alloys up to the beginning of this decade, and the thought-provoking strong criticism by Abaspour and Cáceres (2015) on the conventional interpretation of solid solutions of Mg as random solutions are strongly recommended to the readers.

As Witte (2015) mentioned, the earliest use of Mg was for applications, such as ignition and photography flashes. Interestingly, its application as biomaterial also reaches as far back as 1878. Then, we see a large-scale use of Mg alloys in aviation prior to and during World War II for purely military purposes. During those years, only in the United States the production capacity would make up about a quarter of today's world production capacity of 950,000 tons ( Albright et al., 2002 ; Pekguleryuz et al., 2002 ). The earlier association of the term “electron” with Mg alloys was said to be perhaps due to its bright white light when burning or as a tribute to the ancient alchemical term electrum ( Witte, 2015 ). Although, this term actually originated from the geologically occurring gold and silver (Ag) alloys that were used for coinage by the inventors of money, the Lydians of the Aegean coast of Anatolia.

The review presented here does not claim to cover all aspects of alloy development efforts on Mg. For example, we will not attempt to include the consequences of alloying additions that are related to various processing methods so that the text remains within the permitted limits.

Expectations in alloying studies on Mg go beyond achieving superior engineering properties. Although such properties, if achieved, are certainly welcome, expansion of the use of Mg alloys necessitates at least lessening or, even better, remedying the anomalies/problematic attributes of Mg and its earlier commercial alloys. Without stating these issues on Mg, it would be difficult to appreciate the core aim of the efforts and the directions in the studies focusing on Mg alloys. Therefore, with the aim of serving a broader spectrum of readers, we will first introduce the problematic characteristics of Mg.

This article will next attempt to explain the current approach to recuperate those problematic properties of Mg through changing the stacking fault energy (SFE) of different planes of the hexagonal crystal. The very concept of SFE involves the changes in the free electron density distribution around atoms in solid. Thus, it also becomes necessary to evaluate how the solute atoms behave in changing this distribution in the Mg lattice. Therefore, we will, on the one hand, scrutinize the most recent approach in alloy development, that is, controlling the SFE via alloying element additions, and on the other hand, revisit a generally less known scheme of Miedema that assesses the atomic-level thermodynamic interactions in terms of electron exchange between different atoms of binary solid solutions using the electron gas model of atom. Based on the effects of alloying elements from these perspectives, the possibility of two different types of short range order (SRO) will be proposed here. We will then embark on reviewing some of the most outstanding Mg alloy systems. Although the atomic-level concepts of SFE or Miedema's model are introduced through binary systems, our review will extend beyond the binary systems into alloys that form long-period stacking order (LPSO) phases or quasi-crystals. This is so, mainly because these alloy systems appear to be the most successful ones in terms of their properties, and those concepts cannot be ignored for them. However, it should be emphasized that our purpose is neither to take on the task of implementation of those atomic-level concepts to multicomponent alloys, nor to present all the experimental alloy systems given in the literature in a comparative manner. Needless to say, some remedial contributions to change the problematic properties of Mg can be and have been sought through various processing routes as well. However, we will not shift the attention out of the fundamental solution, that is, alloying.

Revisiting the Fundamental Characteristics of Magnesium

Magnesium is the lightest structural metal. Magnesium and its earlier commercial alloys (e.g., AZ or AM series) have more than few shortcomings that generally manifest themselves together in some combinations. Some of these properties are simply inferior properties as compared to those of aluminum alloys and steels. In this respect, it suffices to recall the low elastic modulus, yield strength, and deformation capacity; sluggish and poor aging response; and inferior creep and corrosion resistance. These constitute engineering properties that may be tackled with, at least to some degree, and with a penalty of reduced final weight saving in application, through part design. Yet, some other properties may be seen as anomalies that require in-depth understanding before seeking remedies through alloying. Those may be briefly named as the tensile/compression asymmetry, pseudoelastic behavior, deformation texture, and inefficiency of recrystallization in removing it, and peculiarities in fatigue behavior.

The slip and twinning systems in Mg are shown in Figure 1 . Perhaps the first anomaly of Mg may be pointed out as its incompatibility with von Misses criterion due to lack of five independent slip systems. Magnesium circumvents this criterion due to twinning that operates concomitantly with the basal slip at room temperature and thus shows, although limited, some plastic deformation capacity. The other slip planes of Mg, that is, prismatic and pyramidal planes, operate sequentially, becoming active over 225°C.

Figure 1 . Slip and twinning planes in magnesium crystal.

Concomitant activation of twinning with slip brings about an anomaly of Mg single crystal. Magnesium displays yield strength asymmetry in compression and tensile modes (a critical assessment given in Barnett et al., 2006 ), the tensile yield strength being much higher than that in compression. Both the room temperature twinning and the yield asymmetry are related to the polar nature of twinning and the critical resolved shear stress (CRSS) values of different twinning planes ( Agnew, 2012 ). It should be noted that the terminology used for the two twinning modes may be somewhat misleading. The tensile (extension) twinning simply is the one that extends an Mg single crystal along its c -axis, while compression twinning shortens. The low CRSS value of what is known as extension (tensile) twinning and the CRSS difference between the two twinning modes and their different Schmid factors ( m ) ( Nan et al., 2012 ; Kim and Park, 2018 ) are telling why the former predominates (CRSS ratio for basal <a> slip, {10 1 ¯ 2} extension twinning, prismatic <a> and pyramidal <c+a> slip: 1:0.7:2:15) ( Barnett et al., 2006 ). The yield asymmetry of a single crystal, when coupled with texture, reveals itself once again in polycrystalline material, begetting an anisotropic material.

Twinning may appear to be a way to divide an existing α-Mg grain into several portions and create strengthening as in grain refinement. However, twinning cannot be activated in Mg when the grain size is well below 1μ ( Wu et al., 2011 ; Zhu Y. T. et al., 2012 ). An additional consequence is that extensive basal slip followed by compression twinning can lead to strain softening as shown in experiments conducted on Mg micropillars ( Yu et al., 2012 ). This is simply because the angular deviation created by compression twinning brings the basal planes, which has the highest Schmid factor, into a favorable orientation for further slip. Thus, twinning is also closely related to the crystallographic texture in deformed structures ( Nie et al., 2013 ).

Twinning asserts itself once again and leads to pseudoelasticity. Upon reversing the stress direction, although not through an infinite number of cycles, detwinning creates what appears to be an elastic, that is, pseudoelastic, behavior. Because, at each cycle, the twinning is accompanied by slip in the same material, not all twins detwin together ( Yu et al., 2011 ). Moreover, twinning is polarized ( Christian and Mahajan, 1995 ), and twinning dislocations cannot behave in a military fashion with exact numbers during every reversal of the stress; thus, the pseudoelastic behavior peters out after some cycles ( Wu et al., 2008 ; Brown et al., 2009 ; Yu et al., 2015 ).

Anomalies of Mg further extend into its fatigue behavior and complicated by twinning and detwinning ( Yu et al., 2011 ), necessitating the interpretation of the stress- and strain-controlled fatigue tests separately ( Sumitomo et al., 2003 ; Hasegawa et al., 2007 ; Mann et al., 2007 ). Because below a threshold grain size twinning ceases, such interpretations on fatigue should also consider the effect of grain size as well as the initial texture of the materials ( Huppmann et al., 2011 ).

Deformation texture becomes particularly emphasized in Mg with a large contribution from its easy twinning. This leads to yet another anomaly in Mg. While texture can be lessened greatly or removed in other systems, once texture is created in Mg and many of its alloys, it becomes persistent even after the conventional remedial treatment of recrystallization. Cell formation during recovery stage does not happen, and consequently, newly forming “recrystallized” grains originate from the already textured parents, thus rendering the texture-removing function of recrystallization process futile. This feature is closely related to lack of dislocation populations on non-basal planes as well as to lower SFE of the basal plane, indicating that the remedial measure is also related to the SFE levels of different planes in Mg.

Critical resolved shear stress values for basal and prismatic planes of Mg show very different reduction rates with temperature, and non-monotonic changes for prismatic planes with temperature and alloy concentration in some systems, as well as anomalous changes with temperature in case of second-order pyramidal planes, have been reported ( Akhtar and Teghtsoonian, 1969 ; Obara et al., 1973 ; Hosford, 1993 ; Christian and Mahajan, 1995 ; Balogh et al., 2009 ; Cipoletti et al., 2011 ). If we look at the room temperature values, CRSS ranges from 5 MPa for basal slip, 10 MPa for extension twinning (2.4 MPa in a report by Yu et al., 2011 ), 20 MPa for prismatic slip, 40 MPa for pyramidal slip, and 70–80 MPa (at 150°C) for compression twinning ( Chapuis and Driver, 2011 ). Therefore, it should be remembered that, at the early stages of deformation, the tensile twins, because of lower CRSS value, are more likely to be observed rather than the compression twins. For details of twinning contribution to the total deformation, the reader should refer to the literature ( Yoo, 1981 ; Brown et al., 2005 ).

Many studies relate the changes in CRSS values and/or in c/a ratio brought in by alloying additions. Indeed, via alloying, CRSS values can change through electronic effects ( Masoumi et al., 2011 ), as well as by geometrically changing the c/a ratio of Mg crystal ( Yoo, 1981 ; Yoo and Lee, 1991 ; Chen and Boyle, 2009 ; Wang et al., 2009 ). The changes in CRSS for different planes may not happen to the same extent ( Kim et al., 2015 ) and depend on the changes incurred due to the alloying elements. Nor the changes in c/a ratio can simply be predetermined based on the atomic size differences of the constituent elements.

In a theoretical geometrical evaluation, c/a ratio undoubtedly alters the CRSS values of different slip planes as it changes the corresponding Schmid factors. Since the pioneering studies by Raynor (1959) , it has come to be said that reduction in c/a ratio promotes non-basal slip activity in Mg. c/a ratio has been related to texture development as well ( Styczynski et al., 2004 ). However, c/a ratio does not seem to be a factor fundamental enough to explain all the observed alloying effects in mechanical behavior in a consistent and a coherent manner. c/a ratio of Mg has been found to decrease for its extended solid solutions prepared via rapid solidification techniques for systems other than the binary Mg–gadolinium (Gd), Mg–yttrium (Y), and Mg–aluminum (Al) alloys ( Hehmann et al., 1990 ). While modulus can change depending of c/a ratio, Chen and Boyle (2009) showed that the strength was not related to the modulus changes in Mg–X [X: Y, Al, zinc (Zn)]. Likewise, explanations on the ease of activation of different twinning modes based on c/a ratio changes in hexagonal close packed (HCP) metals, in general, are highly complex and sometimes even contradictory, creating a need to resort to the involvement of other additional mechanisms such as the ease of atomic shuffling or the ability of twin boundaries to act as sinks for dislocations ( Yoo, 1981 ; Yoo and Lee, 1991 ; Wang et al., 2009 ). It is worth remembering that hcp titanium with a lower c/a ratio ( c/a Mg : 1.624 and c/a Ti :1.58) has CRSS values lower for basal and higher for prismatic slip as compared to Mg ( Raynor, 1959 ).

On the other hand, ab initio calculations do not treat CRSS values as a simple outcome of crystal geometry. The alloying effects go beyond changing the c/a ratio as the dislocation core structure and therefore its mobility and ability to dissociate and, in turn, to cross-slip drastically change with different solute atoms ( Yasi et al., 2010 ; Ando et al., 2013 ; Liu and Li, 2015 ). For example, changes in c/a ratio can be attributed to atomic size changes, especially of Mg atoms, depending on the solute type. Ab initio computations by Chen and Boyle (2009) showed that a and c parameters and c/a reduce slightly in Mg–Zn, in which atomic volume of Mg and possibly of Zn also appeared to be reduced (as will be discussed further), whereas Y slightly increased the lattice volume by changing a and c , without changing the c/a ratio.

The sequential activities, based on different CRSS values and/or temperature, of different slip planes of Mg point out that some of these slip/twinning modes are “softer,” whereas the others can be described as “hard.” It then becomes obvious that the strategy to strengthen Mg or to increase its deformation capacity and even to lessen the propensity to generate deformation texture, as well as the ease of its removal through recrystallization, hinges on establishing the effects of alloying elements and their necessary quantities. If the differences in CRSS values are lessened, it would effectively mean either the “harder” modes becoming “softer” or vice versa . Another way of looking at “hard” and “soft” modes can be based on dislocation characteristics. For example, if thermal cross-slip is facilitated via increasing the SFE of the basal plane, and/or by lowering the SFE of nonbasal planes, a reduced anisotropy in deformation can be achieved ( Moitra et al., 2014 ). If the prismatic and pyramidal slip systems, which do not contribute to deformation at room temperature, are activated, the former provides two and the latter five additional slip systems ( Avedesian and Baker, 1999 ).

The relatively more recent efforts in resorting to the ab initio techniques together with the experimental studies focusing on dilute alloys stem from this perspective. The success of first-principles techniques (density functional theory, embedded atom model, molecular dynamics) in predicting the influences of alloying elements on dislocation behavior, and consequently on the overall mechanical behavior, lies in the fact that they allow consideration of a fundamental property, that is, free electron density distributions and the resulting bond strength and SFE changes.

In order to benefit more from the vast amount of literature involving ab initio techniques regarding the alloying, the reader should be well-versed on SFE and its influences on materials behavior. Therefore, it seems appropriate to remind ourselves the following:

Concepts of Stacking Faults and Stacking Fault Energy

It is well-known that, when stacking close packed layers of atoms to constitute an face centered cubic (FCC) or an HCP model, the difference arises by the positioning of only the third layer, thus …ABCABCABC… stacking gives FCC, whereas …ABABAB… stacking gives HCP. Thus, a mistake in these orders can convert one of these two crystals into the other locally. Such out-of-step stacking can be due to an extra atomic layer [named as “extrinsic stacking fault” (SF)] or, for example, because of condensation of vacancies, a missing layer (“intrinsic SF”). One can define a stacking disorder (SF) perpendicular to any crystal plane and in different directions in it, but for example, in prismatic plane of Mg, a stable SF cannot form as energetically prohibited ( Uesugi et al., 2009 ).

If we make definitions based on the basal plane of Mg, the types of intrinsic SFs are two types, that is, the “growth type” and “deformation” types. The former is a missing layer with shear above it by 1/3[10 1 ¯ 0] (…ABABCBCB…– I 1 stacking), and the latter involving only shear by 1/3[10 1 ¯ 0] (…ABABCACACA…– I 2 stacking). Because SF involves a change in bond angles, a third type is also possible corresponding to stacking across a twin boundary (…ABABCBABABA…– T stacking) ( Weinert, 1997 ). The order of increase in the energies of I 1 , I 2 and extrinsic SF manifests itself in the same order in terms of the number of influenced planes neighboring the SF plane ( Wang et al., 2012 ; Wang W. Y. et al., 2014 ). While I 2 SFE is directly representing an energy barrier to slip, attempt has been made also to correlate the seemingly unrelated I 1 SFE to deformation processes as will be discussed later.

Stacking fault energy, at the fundamental level, depends on the free electron density distribution, a property that changes inevitably with each alloying element, as their contribution to free electron density and/or the lattice distortion they introduce differs. Although a change in the stacking order does not change the coordination number of the atoms at and across the fault plane, at least the bond angles change. Hence, the fault plane, that is, SF, is a more energetic location compared to the planes located in the usual stacking order, in addition to being a plane where free electron density distribution in any direction from one atom to any of the neighboring atoms has also changed. An SF and its energy, as we will focus on later, not only stem from its atomic stacking configuration but also is fundamentally related to the atomic-level thermodynamics.

An SF is by definition bound by two partial dislocations, constituting a two-dimensional defect lying in between. The energy of a dislocation, being the sum of two terms, that is, the missing bond plus the strain energy due to the bent planes immediately neighboring the dislocation, also changes with SFE. Thus, dislocations on planes where SFE is low become more energetic, as the dislocation core size increases with decreasing SFE. Consequently, the ease of dissociation of a dislocation becomes closely related to SFE, getting more difficult as SFE increases, and vice versa . Hence, the prerequisite for creation of an SF is a low-enough SFE allowing dissociation of a full dislocation, relating the size of the SF area between the partials inversely to SFE.

These concepts, namely, the size of SF area and dislocation core size, change all of the mechanical responses of metals through changing the dislocation behavior. Stacking fault energy is related to the ease of birth, glide, cross-slip, and climb of dislocations. The sequential activation of the slip planes of Mg also manifests itself in the computed SFE values [SFE basal < 50 mJ/m 2 ; SFE prismatic = 354 mJ/m 2 ; SFE pyramidal = 452 mJ/m 2 ( Wen et al., 2009 )]. These figures imply that cross-slip and climb for pyramidal slip operate more readily than those for other slip systems because of higher SFE levels ( Li et al., 2013 ). Moreover, the initial glide of dislocations ( Zhao et al., 2006 ), formation of twins, and movement of their boundaries ( Bernstein and Tadmor, 2004 ; Van Swygenhoven et al., 2004 ) are all facilitated with lower SFEs, while climb gets slower, cross-slip restricted, and steady-state creep rate reduced ( Li and Kong, 1989 ; Guo et al., 2006 ). It should also be noted that with larger core sizes, because of larger strain fields of dislocations, in a system of low SFE, while facilitating the movement of an individual dislocation, strain hardening becomes quicker, that is, dislocation movement rapidly becomes more difficult due to the larger core size of dislocations when their populations increase during deformation.

Thus, one would understand that SFE would also change whenever other players/factors are introduced. For example, if the fault plane (SF) involves foreign atoms, if near other crystal defects, when extrinsic factors such as temperature and strain are in play, we may expect SFE to change by some degree. However, all these are not to say that SFE is such an ambiguous parameter that can be ignored. On the contrary, one should remember that SFE is a relative term that can be used in a comparative way when different metals, alloys of a particular metal-base, or different planes of the same crystal are considered. Although there also exists a definition as generalized SFE (GSFE, γ surface), each crystallographic plane has, in essence, its own specific SFE value. Generalized SFEs should ideally be calculated by considering the lattice plane neighboring the SF on both sides, that is, the relaxation of the lattice perpendicular to the SF ( Vitek, 1968 ; Yin et al., 2017 ). The extent of this relaxation is different when considering the SFE of different planes. Furthermore, GSFE values computed by assuming a random solid solution may contain a source of error [e.g., if SRO exists]. Thus, it becomes more useful to compare the individual SFE values of planes that are operative in slip or twinning. It should be emphasized that, in a low-symmetry system such as HCP Mg, SFE of individual crystal planes becomes more distinctive and must be considered specifically. On the other hand, GSFE values are more suitable for interpretations based on Peierls–Nabarro forces ( Moitra et al., 2014 ).

The implications of SFE can be better interpreted through “energy change with respect to the unfaulted atomic stacking” vs. “displacement along a fault vector” plots based on ab initio calculations. These plots show an increase followed by a decrease over the full movement of the fault vector as shown schematically in Figure 2 . More complex three-dimensional representations of lattice response to displacements, namely, GSFE surfaces (γ surface), are also available in the literature ( Wen et al., 2009 ; Yasi et al., 2010 ; Zhang et al., 2013 ). In such a plot if a single curve appears, the maximum (γ USF -unstable SF) ( Figure 2A ) represents the energy barrier for dislocation dissociation and implies that formation of SF is not possible. If the curve shows two maxima, the first one still shows the energy barrier for the formation of an SF, and the trough [γ SF , also termed as γ IS (intrinsic SF)] shows the energy of a stable SF. The second maximum in this case ( Figure 2B ) corresponds to the energy barrier for the formation of a twin. The minima in such plots, although very difficult, can be experimentally determined, while the maxima can be calculated only via ab initio techniques, which are also demanding tasks by any measure. The height of the peaks, that is, ratio of stable and unstable SFE levels (γ SF /γ USF ) would indicate ease of slip, while twinning tendency diminishes as the ratio of the maxima of the two peaks (γ UT /γ USF ) increases ( Wang et al., 2011 ; Muzyk et al., 2012 ). Therefore, in order to reveal whether the birth of dislocations, dissociation into partials, or twinning is facilitated due to a particular alloying element, an evaluation of the changes in the ratios of γ SF /γ USF and γ UT /γ USF on specific crystallographic planes becomes critical. For example, Wen et al. (2009) showed that the unstable SFE for the prismatic plane {10 1 ¯ 10} is one order of magnitude higher than the (0001) basal plane, which effectively points out that creation of <c+a> dislocations is difficult on prismatic planes. It was also shown that the γ USF for the second-order prismatic plane {11 2 ¯ 0} is one order of magnitude higher than the first-order prismatic plane {10 1 ¯ 0}.

Figure 2 . Typical computed GSFE curves. (A) the maximum (γ USF , unstable SF) represents the energy barrier for dislocation dissociation and implies that formation of SF is not possible; (B) if two maxima exist, the first one still shows the energy barrier for the formation of a stacking fault, which means dissociation of dislocation is possible, and the trough (γ SF , also termed as γ IS , -intrinsic SF-) shows the energy of a stable SF. The second maximum in this case corresponds to the energy barrier for the formation of a twin.

As can be understood, developing alloys has reached to the point where assessment and adjustment of dislocation characteristics, and even phase stability in some other systems (e.g., new generation steels), in relation to SFE became imperative. In this regard, ab initio techniques have an exciting power in predicting the SFE changes for specific crystal planes and, in turn, all related changes for an alloy. It is obvious that ductility or strengthening considerations for Mg, in other words, adjusting the relative activities of “soft” and “hard” modes through alloying, has to involve the changes created in SFE(γ) and dislocation core properties as demonstrated in the literature ( Yasi et al., 2010 ; Sandlöbes et al., 2011 , 2012 ; Liu et al., 2017 ; Buey et al., 2018 ).

Effects of Individual Alloying Elements

Thermodynamic ab initio approach and ab initio sfe calculations.

Because of the inherently low strength and ductility of Mg, solid solution strengthening may be regarded as the most important issue before considering the usefulness of all other strengthening mechanisms ( Abaspour and Cáceres, 2015 ) as alloying element selection will influence all other strengthening mechanisms. Overwhelming majority of the literature is on substitutional alloying element additions, ranging in coverage from dilute systems to precipitate forming compositions. One example of much less explored area is Mg alloys containing interstitial elements, in which an interesting example now exists and will be discussed later. It is also interesting to note that those studies mostly consider the solid solutions as random solid solutions. The articles based on ab initio techniques, on the other hand, report the influence of alloying elements in solid solutions from the view of changing SFE values. The ab initio calculations, being highly important and informative, they are not exactly explaining interactions between the host and solute atoms based on atomic-level thermodynamics openly and clearly.

Therefore, we will make an attempt, by referring to the relevant literature, to point out that most of the solute elements do not form random solid solutions due to electronegativity differences, but instead they create what may be termed as electronic effects at the atomic level and consequently create SRO with strikingly different results. Thus, it can be argued that any calculation disregarding this concept and assuming random solid solutions would deviate, to some extent, from the reality.

The ultimate aim is to understand the behavior of each element and then expand this understanding toward designing multicomponent alloy systems. The fundamental approach attempting to explain the effects of individual elements in solid solutions has to be based on atomic-level thermodynamics. The theories on interatomic bond formations date back to Pauling (1960) . Later, the geometrical method proposed by Miedema (1973a , b) ; Miedema et al. (1975) and Buey et al. (2018) following the work by Waber et al. (1963) showed better predictions for solubility or intermetallic formations.

These prediction methods were employing atomic-level thermodynamic parameters, for example, an electronegativity (equivalent to chemical potential) vs. atomic radius diagram ( Waber et al., 1963 ), and chemical potential difference vs. electron density difference at the atomic Wigner–Seitz cell boundaries ( Miedema, 1973a , c ). As we will further discuss, the coordinates in these plots, for a host element of concern, indicate a specific area in the plot for a binary alloy, with great statistical correction over many binary systems, whether a solid solution and/or intermetallic compound is possible, and hence the term geometrical method is used.

On the other hand, the more recent approach in line with that of Miedema's, that is, ab initio techniques, so far based on relatively simple atomistic models and performed for 0 °K, has already proven invaluable in revealing the effects of alloying elements as a reference state. Some of such studies present the free electron density distributions (contour maps) around a foreign atom ( Chen and Boyle, 2009 ; Wu et al., 2016 ) and also reveal the density of states (DOS) for electron orbitals involved in electron exchange ( Chen and Boyle, 2009 ) and calculate the consequent SFE changes created ( Sandlöbes et al., 2012 , 2014 ; Zhang et al., 2013 ; Pei et al., 2015 ; Wu et al., 2016 ; Dong et al., 2018 ), including the influence of van der Waals forces ( Ding et al., 2016 ) on SFEs in Mg. Moreover, some recent studies applied the same approach to dislocation–foreign atom ( Yasi et al., 2010 , 2011 ; Tsuru and Chrzan, 2015 ; Buey et al., 2018 ) or dislocation–dislocation ( Fan et al., 2017 ) interactions with very interesting results.

It seems reasonable to say that the researchers have now a far better understanding on the effects of individual alloying elements as a result of ab initio approaches. The knowledge thus accumulated may be heralding the computer-based alloy design in some not-so-distant future. In conjunction with these efforts, experimental alloy systems started to emerge offering solutions to the shortcomings of Mg. The so-far accumulated knowledge, as Pei et al. (2015) named it, is already close to use a “theory-guided rapid alloy prototyping” approach.

Assessment of Solubility or Compound Formation

Thermodynamic assessment of solid solution hardening can be made more critically based on Miedema's model ( Miedema, 1973a , b , c ; Miedema et al., 1975 ) rather than on Hume–Rothery rules, as the former not only treats the electronegativity in physically less ambiguous way, but also takes the free electron density distribution around the atomic cells into account when calculating heat of formation. This treatment of free electron density distribution of the model also constitutes a central issue in the recent SFE calculations via ab initio techniques.

According to Miedema's model, when a solute atom is added (M-X binary), the system tries to smooth out free electron density distribution in the lattice at the atomic scale in addition to an electron charge transfer. The effect of the solute in these two terms is related to the electronegativity difference with the host and to the number of its valence electrons, that is, the chemical misfit. Moreover, in solid systems, additional energy terms are involved, that is, the misfit strains due to the size differences as well as the shear modulus misfit, thus making the assessment of solid state changes more complicated. Consequently, the bond energy, and in turn, SFE of a crystal plane, is also effected due to the presence of a solute. Computational techniques for solid state have been involving these concepts in calculating SFE values at atomic level with greater precision.

In the mathematical expression of Miedema, the formation enthalpy was expressed as follows:

( Miedema, 1973a , c )

where f (c) is a function of concentration; P and Q are assumed to be constants; e is electronic charge; Δϕ * is the difference in chemical potential for electrons (equivalently the difference in electronegativity or difference between the work functions); and Δ n WS is the difference in the density of electrons at the boundary of the two atomic cells (i.e., Wigner–Seitz cells, which are subject to changes while atoms are changing positions from one equilibrium state to another, a point closely related to SFE; it should also be noted that Wigner–Seitz cell concept cannot be understood if one still assumes a spherical hard ball model for atoms).

The mathematical expression of the Miedema model was later modified in an empirical way for the atomic size factor ( Zhang and Liu, 2002 , 2005 ; Sun et al., 2011 ) and also extended to ternary systems as well ( Dai et al., 2007 ). There may be more examples of its modifications in the literature beyond the knowledge of the author of this section.

Discrepancies in the geometrical predictions of the model when considering the case between transition and non-transition elements were attributed to a negative extra energy term R (explained to be due to hybridization of d and p orbital electrons). Unless a divalent non-transition metal is mixed with a strongly electronegative element, R was assumed to be negligible, that is, R = 0, for example, Mg, and a transition metal ( Miedema, 1973a ).

The heat of formation (Δ H ) determines the nature of the binary mixture. Thus, it also dictates the general constitution of the binary phase diagram, indicating whether a random solid solution (Δ H = 0 ), a system with limited solubilities without any formations of intermetallics (+Δ H ), or a system involving intermetallics (and small solubility), prevails (–Δ H ) ( Miedema, 1973a , b , c ). Let us remember that strongly electronegative metals are those with greater tendency to form negative ions, and the weakly electronegative ones are those with a greater propensity to form positive ions. It follows that as the difference in electronegativity between the constituent elements in a binary alloy increases, a greater tendency to form intermetallic compounds is observed, with an accompanying larger heat release, that is, more negative heat of formation. In such a case, formation of a solid solution is also suppressed. This assessment would also reflect itself in the phase diagram of the mixture, in which more than a single eutectic can be expected if formation of intermetallics is probable. As pointed out by Miedema (1973a) , based on an earlier work of Brewr (1967) ; in the extreme case when the two metals have strong affinity to each other, the mixture, as in the case of Hf and Pt, can be explosive. Albeit, as emphasized by Miedema, the very concept of electronegativity is difficult to establish for metals.

As Equation (1) shows, the two intrinsic terms, namely, the electronegativities of the constituent elements (which is shown to be linearly related to the work function in the original Miedema model) and their contributions to the free electron density of the mixture, determine the enthalpy of formation. The term Δϕ * , created through charge transfer between the two constituent elements, makes a negative contribution to the formation enthalpy of the mixture, thus reducing the total free energy of the system. The term Δ n WS , involves rearrangement of electron density distribution at the atomic cell boundaries (Wigner–Seitz) with the need to smooth it out. This phenomenon requires a complementary change in the Wigner–Seitz atomic cell sizes of both of the elements, therefore constituting a positive contribution term, that is, making the atoms of both elements more energetic as compared to their pure state. The most problematic issue then becomes the complication arising when also taking the size (radius) of the constituent atoms into consideration especially for systems involving the transition metals due to their compressibility levels. Possibility of the two terms, Δϕ * and Δ n WS being interdependent, was thought to be negligible and therefore ignored in the original model ( Miedema, 1973a , c ).

Thus, the arrived geometrical scheme is a plot of the Δϕ * vs. Δ n WS , grouping the binary systems generally into two, with a linear line having the slope of P/Q . Nearly all the binary systems in transition metals that have a negative enthalpy are located above this line, constituting intermetallic forming binaries, and those with positive enthalpy values remaining below the border line, representing those that cannot form compounds and show low mutual solubility. This geometrical scheme was further elaborated in the same article, taking into account the fact that such a border line can be drawn for a specific element (Mg being the one in the original article) twice by crossing each other, because the absolute values of |Δϕ * | and |Δ n WS | (Equation 1) would mathematically necessitate it. By doing so, Miedema's scheme now presents four sectors in the ϕ * vs. n WS diagram, with the upper and lower sectors belonging to binary systems of Mg–X that would show negative enthalpy, and the left and right sectors to those with positive values. Thus, by indicating the position of any element with its own values of ϕ * vs. n WS , a crossover can be generated, which geometrically reveals a crucial information, that is, upper and lower sectors involving those elements that would form intermetallics with the reference element. The graph for Mg has been given as a conceptual plot in Figure 3 ; for quantitative information on each element in this figure, the reader should refer to Miedema (1973a) and Abaspour and Cáceres (2015) .

Figure 3 . A conceptual illustration of Φ* (eV) the chemical potential for electrons (equivalently, electronegativity, or the work function) vs. n WS (d.u., density unit) electron density at atomic cell (Wigner-Seitz) boundary (d.u., density units). The upper (north) and lower (south) sectors indicate the elements that can form intermetallics with Mg, and the left and right sectors involves the elements that do not (data adopted from the refs.: Miedema, 1973a ; Abaspour and Cáceres, 2015 ).

Assessment of Solute Element Additions Based on Miedema's Scheme

The electronegativity differences between the solute and the solvent must have consequences at the atomic level and in terms of electron density distributions. Therefore, most binary systems should show some degree of resistance to form B–B bonds in a system of A–B, which may appear to be a simple solid solution on the respective phase diagram (i.e., considering the limited solubility regions at terminal sections of a phase diagram). This phenomenon was described as SRO in the early work by Cahn and Davies (1960) , in which they also referred to the preceding studies of Houska and Averbach (1959) and Suzuki (1962) . Short range order was also reported in earlier studies on binary Mg alloys, namely, in Mg–tin (Sn) ( Henes and Gerold, 1962 ; van der Planken and Deruyttere, 1969 ), in Mg–(6.4 at%) Er and local order in Mg-(2.9 at.%) Gd ( Gencheva et al., 1981 ), and in Mg–Zn ( Akhtar and Teghtsoonian, 1969 ). Since then, a number of relatively recent studies on lean binary Mg alloys also focused on SRO ( Blake and Cáceres, 2008 ; Abaspour and Caceres, 2013 ; Abaspour and Cáceres, 2015 , 2016 ; Abaspour, 2014 ; Yang et al., 2014 ; Zhang et al., 2014 ). According to Abaspour and Caceres (2013) , SRO was also claimed in previous studies ( Henes and Gerold, 1962 ; Safranova et al., 1977 ) based on small-angle x-ray scattering. However, without refuting their claims, it should be borne in mind that Suzuki segregation ( Suzuki, 1962 ) can also create similar x-ray scattering results. Many of the counter arguments on the effects of SRO were dismissed by Abaspour and Cáceres (2015) . However, one that involves segregation of the solutes to dislocations does not seem to be easily dismissible. Serrated flow observed by these authors also testifies to this possibility, without going to the extreme example ( Abaspour and Cáceres, 2015 ) of a Cottrell atmosphere.

Short range order can be viewed as a case where B–B bonds are not allowed in a binary A–B system. The phenomenon of temperature-independent flow stress in some Mg–X alloys, that is, “athermal component of solid solution strengthening,” has been attributed to SRO ( Akhtar and Teghtsoonian, 1969 ; Abaspour and Cáceres, 2015 , 2016 ; Abaspour et al., 2016 ). In essence, the phenomenon is an extra strengthening mechanism that cannot be explained based on simple solid solution strengthening ( van der Planken and Deruyttere, 1969 ). Therefore, the physical meaning of SRO requires in-depth analysis in terms of inter atomic effects. As the term implies, SRO is limited to each A–B–A (letters representing atoms, not atomic layers) sequence in an α-Mg grain and effectively constitutes stronger obstacles to dislocation motion as compared to a case where the solute atom is just a substitution in a random solid solution. Whether the interaction of such solute atoms in SRO with dislocations can be considered as a short-range or long-range interaction is debatable as it also depends on the concentration of the solute. However, such types of obstacles would be expected to be more resistant to relatively high temperatures unlike the short-range interactions of dislocations, that is, as for the dislocation–dislocation interactions, which can be overcome readily with temperature effects. Consequently, presence of SRO can become especially useful for Mg to overcome its shortcomings such as low strength and elasticity modulus and poor creep resistance. The contribution of SRO to strength with high resistance to changes in temperature was demonstrated via compression and stress relaxation tests conducted at various temperatures ( Abaspour and Caceres, 2013 ; Abaspour, 2014 ; Abaspour et al., 2016 ) and via creep experiments ( Abaspour and Cáceres, 2015 ).

The following experimental observations were reported by Abaspour et al. for Mg–X [X: Y, Gd, Ca, Zn, Sn, antimony (Sb), and Al] binary systems: an initial linear strengthening at constant temperature tests; for some alloys, an increasing strength at higher temperatures and little or no stress relaxations. Studies by Abaspour (2014) and Abaspour and Cáceres (2014 , 2016) showed that temperature dependence of the strength of some Mg–X [X: Al, Zn, Sn, Y, Gd, neodymium (Nd)] alloys displayed an athermal regime at low strain levels up to some different temperature range and to varying levels. The same workers further claimed that there was even a strength increase within a temperature range in the case of Mg–X (X: Y, Gd, Nd) (see Figures 2, 3 in Abaspour and Cáceres, 2016 ). These observations, which cannot be explained based on an ordinary solid solution, were all attributed to SRO in those alloys ( Abaspour and Cáceres, 2016 ; Abaspour et al., 2016 ). The potential of these alloying elements to develop SRO in Mg was given, based on Miedema's model, in the following order ( Abaspour and Caceres, 2013 ; Abaspour and Cáceres, 2016 ; Abaspour et al., 2016 ):

Y, Gd > Nd, calcium (Ca) > Zn, Ag, Sn > Al > Sb, strontium (Sr)… ( Abaspour and Caceres, 2013 ; Abaspour and Cáceres, 2016 )

This ranking given by Abaspour and Cáceres contradicts the implications of ab initio calculations of diffusion coefficients for the same binary systems:

D Mg−Ca > D Mg−Zn > D Mg−Sn > D Mg−Al … ( Ganeshan et al., 2011 )

The apparent contradiction may be due to the assumption of “random solid solutions” employed by Ganeshan et al. (2011) . However, the bond strength calculations by Chen and Boyle (2009) also contradict the experimental values given by Abaspour and Cáceres (2015) for Mg–Zn. It seems that the interpretation of SRO may not be straightforward in every case and requires more detailed insight using the available ab initio calculations.

Assessment of Interatomic Bonding in Solid Solutions of Mg—Two Types of SRO

Abaspour and Cáceres (2015) disagreed with the approach to explain the solid solution strengthening incurred by Y and Gd elements (the athermal strengthening effect) in Mg–X systems via a valence mechanism as proposed by Chen and Boyle (2009) . However, their objection seems unwarranted. An ab initio study by Chen and Boyle (2009) on binary systems, namely, Mg–Al, Mg–Zn, and Mg–Y, and on Mg–Li ( Jin et al., 2011 ), showed that the interatomic bonding possessed different characteristics depending on the planes and directions in pure Mg, as well as in these lean binary alloys.

Interestingly, pure Mg was found to have, although very weak, directionality in bonds within the basal plane and perpendicular to it, the latter being stronger. The DOS (local DOS) calculations of pure Mg is consistent with several other reports ( Wang et al., 2007 ; Peng et al., 2008 ; Kumari and Verma, 2018 ). It was shown that such directionalities were also displayed in Mg–Y ( Chen and Boyle, 2009 ) and Mg–Al ( Chen and Boyle, 2009 ; Ganeshan et al., 2011 ; Jin et al., 2011 ) systems, the latter being weaker than the former but both being stronger than those in pure Mg to varying degrees ( Chen and Boyle, 2009 ). It should be stated that Mg acts weakly electronegative in Mg–Y ( Stanford et al., 2015 ) and forming hybridized bonds with Y. Likewise, although Mg behaves electropositively in Mg–Al system, the bonding is again only weakly hybridized as the DOS calculations for Al in Mg–Al showed a reduction only for its highest energy levels ( Ganeshan et al., 2011 ).

Mg–Zn system, on the other hand, did not show directionality as also indicated in some studies ( Ganeshan et al., 2011 ; Garg et al., 2018 ). Similar cases in Mg–Li ( Jin et al., 2011 ) and in Mg–Ca ( Ganeshan et al., 2011 ), that is, a general depletion around the solute atoms and a general homogenization in their electron densities for all energy levels, were computed for Mg–Li and Mg–Ca, where the electronegativity differences are opposite to that in Mg–Zn, that is, Mg acting electronegatively and Li and Ca acting electropositively. Moreover, Zn slightly reduced a and c parameters and c/a ratio, whereas Y, while slightly increasing the lattice volume by changing a and c did not alter c/a ratio. The former case effectively meant a reduction in atomic volume of Mg (and possibly for that of the solute atoms as discerned from their DOS calculations), and the latter, an increase ( Chen and Boyle, 2009 ; Stanford et al., 2015 ).

The studies by Chen and Boyle (2009) and by Jin et al. (2011) further showed via computational methods that the bond strength in a solid solution dominated by the shared electrons (computed as bond order–BO–). When naming the bond types, they referred to the earlier definition by Bader (1990) , who suggested that all bonding interactions fall into the following categories, as has been confirmed by the recent ab initio computations: (i) the shared-electron interaction, creating covalent (localized electron sharing) and metallic bonds (dilocalized electron sharing), and (ii) the closed shell interaction, leading to ionic as well as weak bonds.

An increasing BO was interpreted to mean an increasing strength through the series Mg–Zn, Mg–Al, and Mg–Y ( Chen and Boyle, 2009 ). In Mg–Zn system, there appeared to be no covalent bond formation specific to the presence of Zn [likewise in Mg–Li ( Jin et al., 2011 )] as the electron localized function (ELF) maps (also known as charge density contour maps) indicated. Furthermore, DOS calculations pointed out that all electron densities (more in p orbital than that in s ) around Mg atoms neighboring Zn reduced, in addition to the removal of the mild covalency within the basal plane of Mg (existed in pure Mg) around the Zn atom. However, the mild again covalency between Mg atoms in z direction remained unchanged. The DOS calculations for Zn in Mg–Zn ( Ganeshan et al., 2011 ), Sn in Mg–Sn, and Li in Mg–Li also showed an overall reduction and homogenization for all energy states of the solute atoms, further indicating a possible size reduction in the atomic sizes of the solutes as well. Therefore, the atomic size reduction both for Mg and the solute atoms may be interpreted as the birth of an extra strain field around the Mg atoms surrounding each solute in these binary systems. This strain field would require consideration in addition to the one that would normally exist due to the size difference of Mg and solute atoms. This reduction in the atomic size of Mg was also pointed out by Chen and Boyle (2009) . However, Chen and Boyle discerned this atomic size reduction indirectly and on the basis of crystal parameter changes, without relating to their own DOS calculations, which effectively showed the electron contribution from all orbitals of Mg in Mg–Zn. The proposed extra lattice straining due to large electronegativity difference between Mg and the solute atoms was also foreseen for the system of Mg–Sn in another study ( van der Planken and Deruyttere, 1969 ), constituting another example of SRO without covalency (hybridization).

Regarding the Mg–Y system, Chen and Boyle (2009) showed that no significant DOS change occurred in s and d orbitals of Mg, whereas its p orbital showed some increase, which was interpreted as hybridization between Mg and Y atoms, involving p and d orbitals, respectively (the calculated DOS of d orbital of Y in Mg–Y being strikingly dominant), as well as stronger directionality in the bond structure. They further confirmed through Cauchy pressure evaluation that in one direction the value was negative, also indicating directionality in the bond strength.

The proposed two SRO mechanisms also comply with the expected SFE changes in two different cases. Zn should increase I1 SFE due to reduced average atomic size ( Pei et al., 2015 ), while Y showing an opposite trend, and indeed reported to be so ( Sandlöbes et al., 2014 ). It may further be expected that the influence of hybridized bonds would not be uniform on the SEFs of different crystal planes, whereas the non-hybridized type would create more uniform changes, that is, either increase or decrease to similar extents. A critical evaluation of SFEs for elements representing two different SRO types showed that the expectation is largely fulfilled ( Moitra et al., 2014 ; Shang et al., 2014 ; Zhang et al., 2014a ; Dong et al., 2018 ). It seems that the implications of atomic size changes in terms of changes in a, c , and c/a ratio are also worth considering.

In one case, based on the DOS reductions in all orbitals of Mg and the consequent change in its atomic size, as in Mg–Zn and Mg–Sn, it may be interpreted that Mg behaved as a strong donor (more electropositive) as compared to the case of Mg in Mg–Y. Thus, in this SRO case, if the electronegativity difference is large enough between Mg and solute atoms, the charge transfer is stronger, leading to homogenization and an accompanying reduction in all DOS levels. Hence, the consequence is a reduction in atomic sizes, without resorting to hybridization. Such Wigner–Seitz atomic cell size changes were said to be large in Miedema's model ( 1973c ). This can be envisaged to lead to an extra strain field (in addition to the atomic size difference of the solute) involving both the Mg and the solute atoms whenever they are neighbors and consequently additional strengthening as compared to the one expected from a random solid solution, whereas if hybridization of electron orbitals takes place, this extra strain field is absent or negligible. In this case, the SRO and accompanying strengthening are only due to the increased bond strength (covalency) between Mg and solute element.

Thus, it may be concluded that the strengthening mechanism of individual elements may depend on the way the electrons are shared. In both non-hybridized and hybridized cases, SRO forms. However, the degree of effectiveness in increasing strength differs, being stronger if hybridization exists. This view should also be taken to emphasize the importance of the purity of the alloys prepared for experimental comparisons ( van der Planken and Deruyttere, 1969 ). In the case of Mg–Y, that is, hybridization, while increased covalency increases strength, the alloy may be expected to become more brittle according to the criteria (brittleness: R G/B > 0.5) by Pugh (1954) . However, Chen and Boyle (2009) showed that the strengthening effects in case of Al, Zn, and Y did not seem to be related to the changes in bulk moduli, and therefore despite the modulus-based criteria of Pugh, brittleness did not prevail in Mg–Y (R G/B > 0.605).

To the best knowledge of the author, DOS calculations and ELF maps are unfortunately not available in the literature for all Mg–X binary systems to firmly conclude the presence or absence of covalency. The atomic size change is a complex phenomenon as it may be necessary to consider more than the immediate neighbors of the solute atom, in addition to the original atomic radii and concentrations. The DOS calculations and constructions of ELF maps seem indispensable for each binary system for a more complete understanding.

The phenomenon of SRO elegantly indicates the possibility for an approach to design alloy systems in a subtle and economical way. For example, α-Mg solid solutions containing only 1% addition of Y, rare earth (elements) (RE), or Ca were shown to be competitive in flow behavior with the traditional alloys, such as QE22 and ZE41, and be better than AE42 and AS21 ( Abaspour and Cáceres, 2016 ). Abaspour and Cáceres, with reference to the studies by Zhang et al. (2014) , pointed out the importance of SRO and, in turn, the selection of the alloying element, especially for cast structures showing inherent coring. The overall strength levels of such cast parts were said to dependent on the strength level of the weakest regions of what was described as percolated structures that were made up of weak solid solution regions (interiors of the cored grains) and interconnected strong grain boundary intermetallics.

When accounting for their observations, Abaspour and Cáceres (2015) disputed any role of the mechanisms, such as pinning of edge dislocations with mobile solute atoms, atomic size effect on the diffusivity, or dynamic precipitation of thermally stable precipitates. However, there exist atomic resolution imaging studies, explaining the temperature resistance of the strength on the basis of solute segregation (said to be driven by the need to reduce the twin boundary strain energy minimization) to mechanical twin boundaries in Mg–Gd, Mg–Gd–Zn ( Nie et al., 2019 ), Mg–Y ( Somekawa et al., 2017 ), Mg–Ca, and Mg–Zn ( Somekawa et al., 2014 ) systems. Such solute segregations themselves were shown to be ordered along the twin boundaries and to have occurred in short annealing times. If one treats the coherent twin boundary planes as SFs, a justifiable likeness as only the bond angles change across the plane, then this segregation may be regarded as Suzuki segregation. There has been suggestions in the literature to use this type of segregation as an alloy design criterion based on ab initio calculations ( Zhang et al., 2014b ).

Whether this order accompanying segregation to the twin boundaries can be described as a local SRO is a subject for discussion. However, the very existence of the alloying element segregation along the twin boundaries effectively means that they diffused from the nearby matrix regions to these boundaries. Whereas, the original claim ( Abaspour and Cáceres, 2015 ) was that SRO-forming solutes were stable to the extent that temperature changes had little effect, if at all, on their mobility. Hence was the athermal nature of the strengthening effect of SRO. However, this way of questioning is not meant to dismiss the reality of SRO. Examinations of regions away from the twin boundaries in the same α-Mg grains were not given in those reports that presented segregation to twin boundaries. Seeking the presence of SRO away from such twin boundaries would reveal if this segregation and resulting stabilization of the twins were solely responsible for the observed strengthening or were an additional contribution to an already existing SRO effect.

The explanations based on SRO alone in Mg alloys can also be strengthened via conducting some advanced imaging techniques. In such a study on Mg–Zn and Mg–Y systems ( Stanford et al., 2015 ), the alloys were defined as random solid solutions based on tomographic atom probe maps. However, those alloys had very rich solute concentrations, and even then, the majority of solute atoms were a few atomic distance apart rather than presenting a readily noticeable solute–solute neighboring. Moreover, despite the larger atomic size of Y and much richer concentrations of Mg–Y, perhaps due to the extra strain field created by Zn in Mg–Zn, the average nearest neighbor distance between Zn–Zn was almost double compared to that of Y–Y. It is fair to say that further elaborate imaging studies would contribute to our understanding greatly.

SFE-Based Assessment on the Effects of Alloying Elements in Mg–X Systems

First, it should be recalled that SFE for a given crystal plane is strongly influenced by the interatomic electron density distribution and therefore influenced by all atomic scale parameters. It is not a priori that all the SFE values of different planes in a system will follow the suit of change in the SFE of a particular plane under the influence of a particular solute ( Yin et al., 2017 ). As to the GSFE calculations, an important assumption in the currently employed ab initio techniques is that a random solid solution is assumed (Equation 4 in Yin et al., 2017 ). Considering the small size of the atomic models used in calculations, whether this makes a great difference or not is debatable but not unlikely. In this respect, individual SFE calculations may be considered more reliable than those for GSFE.

Several studies on SFE calculations are particularly comprehensive in terms of the number of alloying elements considered ( Moitra et al., 2014 ; Shang et al., 2014 ; Yuasa et al., 2015 ; Dong et al., 2018 ). Pei et al. (2015) , in an attempt to devise a practical guide to alloying, plotted qualitative relationships between the I 1SFE in Mg–X and the relative atomic volume, atomic number, I 1SFE of the solute, bulk modulus, and electronegativity of the solute for 18 elements. Similar reports can also be found in the literature ( Wen et al., 2009 ).

Among the SF types, I 1SFE has been said, although not unanimously, to be indicative of the deformation capacity of the Mg–X systems based on computations as well as observations on Mg–Y ( Sandlöbes et al., 2011 , 2014 ; Agnew et al., 2015 ). Although, I 1SFE does not reveal an energy barrier to slip, its formation is regarded as a source for generation of nonbasal, <c+a>, dislocations, providing a step for slip at room temperature. Therefore, if I 1SFE is low I 1 -type SFs form, the proposed mechanism is assumed to work and explain the ductility imparted by Y (and REs for that matter). A strong criticism to this proposal came from Yin et al. (2017) , indicating that necessary number of I 1 type cannot be generated by slip, and a large population of I 1 SF prior to deformation is necessary to render the mechanism feasible. An alternative mechanism was also put forward by Kim et al. (2015) who, by using molecular dynamics simulation, suggested different level of changes in CRSS values associated with Peierls potentials for pyramidal plane and a very complex movement of leading and trailing partials in a comparative study on Mg–Y and Mg–Al.

According to the findings of Yin et al. (2017) , Zn was the least effective element in reducing both basal and pyramidal I 1 and I 2 SFEs (no effect on basal types), and Al moderately reduced the basal SFEs while not changing the pyramidal types; Y created the most effective reductions as compared to Al and Zn. These findings, when considered together with the previously mentioned results by Chen and Boyle (2009) , may be indicating that SFE reduction becomes more effective as the ranking of interatomic bond between the solute and Mg goes from lack of covalency, that is, Mg–Zn, to weak covalency, that is, Mg–Al, and finally to strong covalency (hybridized bonds) as in Mg–Y.

As to the computed GSFE values, the reports for a wide range of alloying elements for binary Mg alloys are unfortunately not free from contradictions, for some elements even giving opposite trends as can be seen by comparing the values given in Wang et al. (2013) , Moitra et al. (2014) , Shang et al. (2014) , Wang W. Y. et al. (2014) , Zhang et al. (2014) , Yuasa et al. (2015) and Dong et al. (2018) . Having summarized the effects of individual alloying elements in Mg–X systems based on the existing literature that relies on atomic scale thermodynamics, or on first-principles calculations revealing SFE values, we will now attempt to indicate the relationship between the atomic number, size, and ΔΦ * , Δ n WS , and SFE in the periodic table. While Miedema's model considers all the elements in a single plot collectively, we will consider the elements along individual periods of the table.

In order to understand the general trend in the periodic table, several relevant plots have been given in Figures 4 – 6 . The well-known electronegativity change by atomic number has been given in Figure 4 as a reminder that there is an overall trend of increase within each period. The intensity of increase appears to reduce as the period number increases. On the other hand, the plots of atomic number ( Figure 5A ) or size ( Figures 5B,C ) vs. n WS or Φ * showed clear modulations, each “inverted parabola” belonging to a period. An inverted parabolic increase in the plots of I 1SFE (SFE values from Wang W. Y. et al., 2014 ; Dong et al., 2018 ) vs. atomic number ( Figure 6A ) or size ( Figure 6B ) for each period also exists. Figure 7 shows the changes in in Φ * ( Figure 7A ) and in n WS ( Figure 7A ) vs. I 1SFE (Φ * and n WS values are from Miedema (1973a) , Abaspour and Cáceres (2015) , Buey et al. (2018) ; SFE values from Wang T. et al., 2014 and Dong et al., 2018 ). Although a graphical illustration has not been given here, it was found that I 2SFE also showed a similar relationship with Φ * and n WS , whereas GSFE did not show any specific trend (perhaps due to insufficient data). The increase in SFE as the Φ * increased may be interpreted due to an increasing binding force between the solvent and solute atoms. On the other hand, the increase in SFE vs. n WS plots may be attributed to a relatively more polarized electron density distribution at Wigner–Seitz atomic cell boundaries.

Figure 4 . The relationship between the Pauling scale electronegativity values with atomic numbers (data set from: https://en.wikipedia.org/wiki/Electronegativities_of_the_elements_(data_page) with reference to: L. Pauling, The Chemical Bond , Cornell University Press, Ithaca, New York, 1967).

Figure 5 . The plots of (A) atomic number vs. n WS and Φ* (for clarity, the element names are only given for one data set, Φ*); (B) atomic size vs. Φ*; and (C) atomic size vs. n WS . Note that the modulations correspond to individual periods in the periodic table ( n WS and Φ* values are from Miedema, 1973a ; Abaspour and Cáceres, 2015 ).

Figure 6 . The plots of I1 SFE vs. (A) atomic number, and (B) size showing modulations (SFE values from Wang T. et al., 2014 ; Dong et al., 2018 ).

Figure 7 . The relationship between the computed values of I1 SFE with (A) Φ*; and (B) n WS . (Φ* and n WS values are from Miedema, 1973a , b ; Abaspour and Cáceres, 2015 ; SFE values from Wang T. et al., 2014 and Dong et al., 2018 ).

The parallelism between n WS and Φ * against the atomic number and radii further testifies Miedema's original hypothesis regarding the interdependency of the two terms. The linear relationship between the n WS and Φ * was already known due to Miedema. These trends also indicate the relationship between the I 1SFE and the values of n WS and Φ * as atomic scale thermodynamic parameters. Pei et al. (2015) have shown, for presumably a single period (elements were not stated), that I 1SFE in Mg–X increased as the electronegativity of the solute increased.

The inflection points in Figure 6 as well as in Figure 7 correspond to about the middle position in each period, that is, about the midrange in transition metals. This intriguing feature requires further evaluation. If compared with Miedema's plot ( Figure 3 ), it can readily be noticed that all the elements of the upper (north) sector are located in the second half, namely, the decreasing part, in the Φ * , n WS , I 1SFE vs. atomic number plots, and reverse their side in plots vs. atomic size, whereas the elements located in the lower (south) sector of the Miedema plot reside on the reverse half of the same plot in each case. By taking into account the findings of ab initio studies (DOS calculations and the contour maps), it may be deduced that the elements that are likely to form the non-hybridized type SRO with Mg and those that form hybridized type SRO reside on the opposite sides in these “inverted parabolic” plots for each period. As such, it appears to be logical to suggest that the question of what type of SRO forms can be answered depending on the position of the candidate solute element on any of these plots involving the n WS , Φ * or I 1SFE . It may be suggested that if the size difference is relatively smaller and electronegativity is larger, the tendency to form non-hybridized bond type is greater, and vice versa .

Based on the interpretation of these plots, the possibility of using a currently available measurement technique, that is, Kelvin probe force microscopy (KPFM), may be suggested when assessing the SFE changes especially in studies involving multicomponent alloys (Φ * was said to change linearly with Φ, the work function, of the constituent atoms) and that the electronegativity and chemical potential for electrons in an atomic cell were equivalent ( Miedema, 1973c ; Abaspour and Cáceres, 2015 ). Ab initio computations are rather difficult ( Pei et al., 2015 ) and currently not capable of computing SFE in models involving several different solute atoms [few studies considered two solute atoms together ( Kimizuka and Ogata, 2013 )]. Kelvin probe force microscopy, because it measures work function (Φ), that is, the equivalent ( Miedema, 1973c ) of Φ * in Equation (1), may be useful in understanding the SFE changes indirectly as compared to some reference materials, be it pure Mg and/or a binary alloy of known SFE. Because SFE changes are invaluable in selecting alloying elements, this practical measurement technique may prove useful in designing multicomponent alloy systems.

Relationship between electron work function (EWF) and material properties, such as strength and elastic modulus for metals and alloys, was demonstrated ( Halas, 2006 ; Hua and Li, 2011 ; Lu et al., 2018 ). Liu and Li (2015) , via ab initio calculations, showed that both I 1 and I 2 SFEs increased with EWF and that alloying Mg with the elements having lower EWF compared to Mg would impart strengthening as well as ductility and with the other elements, while increasing strength, and lower ductility.

It is thus reasonable to suggest that an understanding of alloying effects has already been established in relation to EWF, which can be measured via KPFM. Admittedly, this knowledge basis currently stems from the ab initio calculations rather than KPFM as a practical method. One impediment when employing KPFM may be the inevitable surface oxide on samples. However, if relative values are to be considered rather than seeking absolute values, KPFM readings may be promising for comparison purposes between different systems.

Doping Magnesium With Oxygen

As a counterintuitive alloying approach, intentional addition of oxygen into Mg has been arguably the most interesting attempt in the history of Mg alloys. Doping Mg with oxygen results in many interesting properties and may also be taken to indicate the potential of dilute systems involving interstitial atoms.

A recent study ( Kang et al., 2016 ) showed that dilute concentrations of oxygen, as an interstitial element, yielded highly surprising remedial effects on the problematic properties of Mg, namely, an increased strength and deformation capacity, removal of the yield asymmetry, and even improved corrosion resistance. It has been postulated that, as a non-metallic addition, oxygen would form interatomic bonds that may be strongly ionic/covalent in character and increase strength ( Kang et al., 2016 ).

Kang et al. (2016) succeeded in mono atomic oxygen addition to Mg by employing the dissociation tendency of nanosized TiO 2 over 400°C when in molten Mg and detected ~0.3% at. oxygen at a depth of 15–18 μ in solidified state after removing the surface oxide layer. Their first report covered pure Mg, Mg–Al, and Mg–Zn systems with oxygen additions. Among them, Mg–Zn–O system showed additional extraordinary features, such as more than 50% elongation to failure without apparent twinning, a yield drop phenomenon akin to simple low carbon steels, and, strikingly, non-basal slip in submicron-sized grains. Thermal conductivities of all oxygen containing alloys were also shown to have increased.

Two of their following studies on Mg−9Al-O alloy also reported a higher oxygen content in β-phase (~3.86% at. in Mg 17 Al 12 ) than in α-Mg (~0.79%), leading to increased d -spacings in both phases and consequently a better match ( Kang et al., 2017 , 2018 ) and stability at the β/α interface, disappearance of the β/α eutectic, and refinement of β-phase. Presence of oxygen brought about benefits in the mechanical properties as compared to Mg−9Al, namely, 30% improved yield strength, 41% increased UTS, doubled elongation to failure, ~10% increase in elastic modulus, and fracture toughness. Albeit, their claim regarding the formation of so-called “reticular” phase during annealing treatments ( Kang et al., 2018 ), due to lack of verification via an irrefutable method, needs substantiation. This reticular phase may turn out to be nothing more than an oxide phase.

To our best knowledge, there exist no studies yet as to the changes incurred in SFE by dissolved oxygen atoms in Mg matrix or an evaluation with actual figures of formation enthalpy of such a solid solution, although based on the evaluations by Pei et al. (2015) , due to the very high electronegativity value of oxygen, a large increase at least in I 1 SFE value of Mg–O can be expected. This foreseen increase would conform to the plot given by Pei et al. (2015) that shows an increase at least in I 1 SFE with average atomic size reduction in Mg–X (Mg–O system should have a decrease in average atomic size according to Figure 3 in Pei et al. (2015) . The experimental observation as to lack of twinning ( Kang et al., 2016 ) seems to support these expectations.

Furthermore, because of the large electronegativity difference between Mg and oxygen, a dilute system of Mg–O is highly likely to form SRO. Based on the discussions earlier, directionality in bonding around oxygen atoms would not be expected. It may also be thought that, through binding, more of the available free electrons of Mg that would otherwise contribute to the corrosion potential may also be the reason for the observed ( Kang et al., 2016 ) improvement of the corrosion resistance in Mg–O system. Such interpretations may render all the beneficial effects of this dilute binary alloy system understandable, but a demonstrated explanation through ab initio techniques could prove highly useful.

The potential beneficial effects of dissolved oxygen deserve exploration at fundamental level and in different alloy systems, be it Mg or other metals. In essence, the effect of oxygen in solid solution has long manifested its potential also in other well-known metallic systems. CP (commercial purity) titanium serves as an engineering material owing its strength level to oxygen in solid solution at ppm levels. Yet another commercially available example is oxygen-free copper, a material that would otherwise be hard and brittle. Even just these two materials clearly point out that addition of oxygen in trace amounts has the potential to create striking changes in metals including Mg. Perhaps the down side to the idea is the inherent difficulty in producing bulk quantities of materials containing controlled and dilute amounts of oxygen. Coupled with this difficulty, the highly problematic issue of finding an economical monoatomic oxygen source may continue to stand on the way to utilization of this approach. Formerly, addition of nitrogen into Mg was also attempted ( Kaya et al., 2003 ). Despite the disappearance of the eutectic morphology in the microstructure as in oxygen addition, the attempt was probably a failure in terms of supplying monoatomic nitrogen into the molten metal due to employment of simple gas purging.

Ultrastrong Magnesium Alloys

Because comparable to the high-strength steels, the strength levels achieved in some Mg alloys deserve the definition of “ultra.” For example, owing to nanocrystalline structures containing LPSO phases, yield strength level as high as 600 MPa was reported in rapidly solidified powder metallurgy products ( Inoue et al., 2001 ; Kawamura et al., 2001 ). More complex but again Y- and RE-containing, a composition [Mg−1.8 Gd−1.8 Y−0.7 Zn−0.2 zirconium (Zr) at.%] also showed a high yield strength of 473 MPa in aged condition ( Homma et al., 2009 ).

A hot-rolled Mg−8.5 Gd−2.3 Y−1.8 Ag−0.4 Zr (wt%) with a yield strength of ~575 MPa ( Wang et al., 2010 ; Jian et al., 2013 ) and Mg−8.2 Gd−3.8 Y−1.0 Zn−0.4 Zr alloy with a proof stress of 426 MPa ( Xu et al., 2012 ) and an earlier example of alloy extrusions in the Mg–Al–Zn–Si–RE system with yield strength levels of >500 MPa ( Chang et al., 1986 , 1987 ) can also be considered in the ranks of the ultra-strength alloys, albeit these high strength levels were not accompanied by high deformation capacities, which were typically <10%.

One study, among those that reported ultrastrong levels, is particularly interesting because of its implications toward developing high-strength Mg alloys. The achieved strength level (σ y ~575 MPa, UTS ~600 MPa, and 5.2% uniform elongation) was attributed to finely spaced SFs by Jian et al. (2013) . As such, because the alloys contain abundant SFs to start with, this alloy system may also serve as a test case to show if I1 -type SFs really play an important part in increasing deformation capacity as suggested in Sandlöbes et al. (2011) , Sandlöbes et al. (2014) , and Agnew et al. (2015) . In this alloy, presence of such nanospaced SFs was proposed as an effective means to increase strength without losing the modest level of ductility even after multipass rolling. It appears that the achieved properties simply depend on the adjustment of SFE. The same study also suggested an interesting deformation mechanism, supporting the findings of an earlier work ( Liao et al., 2004 ). The deformation was said to have changed mode and became SF-mediated instead of slip-dominated after reaching a total deformation range of 30–50% reduction as the SF widening started to operate ( Jian et al., 2013 ). The foundation of this explanation is none other than Suzuki segregation.

The composition of this interesting alloy is akin to those that generate LPSO phases as discussed below. However, it is also worth noticing that despite the proliferation of SFs and presence of the main player elements in LPSO formation, perhaps due to the level of SFEs not being at a necessary critical range, the alloy composition with nanospaced SFs did not create LPSO phases. Considering the fact that the strength level of this structure is as high as those that contain LPSO phases leads to an intriguing question. Is the ultrastrength level achieved in composition with LPSO phases really due to these so-called strengthening particles or only a result of presence of multitude of SFs in the same structures? This view is admittedly simplifying the comparison; however, it appears that with or without LPSO phases, so long as the SFs proliferated the strength can reach to ultra levels.

A category of Mg alloys with outstanding strength levels is found within Mg–Zn–RE [or Mg–TM ( transition metal )–RE] system involving LPSO phases. These may be viewed as the succession of those structures that involve nanospaced SFs without forming another phase as mentioned above. We will now embark on their discussion next.

Systems Containing LPSO Phases

The earliest observation on LPSO in Mg alloys may be ascribed to the report by Luo et al. (1994) on Mg–Zn–Zr–RE system. Many studies also refer to the report by Kawamura et al. (2001) as the precursor study on LPSO phases. Although neither the term LPSO was mentioned nor their morphology presented in that study, superior room and high temperature strengths, relatively good deformation capacity, and high strain rate superplasticity were reported for Mg–Zn–Y system. Later on, the alloys forming LPSO phases proliferated and generally expressed as Mg–TM (transition metal)–RE systems ( Zhiping et al., 1994 ; Yokobayashi et al., 2011a , b ; Kishida et al., 2012 , 2013 ; Xu et al., 2016 ). Existing literature on alloys involving LPSO phases collectively reports high strength ( Kawamura et al., 2001 ; Hagihara et al., 2010a , b ) and improvement in deformation capacity, as well as in creep ( Hu et al., 2016 ; Xu et al., 2016 ) and corrosion resistance as common characteristics, as compared to AZ31, WE43, ZK60, and ZX60 ( Xu et al., 2016 ) alloys. These improved mechanical properties were generally achieved with small additions of Zn and RE, for example, 1 at.% Zn−2 at.% RE ( Nie et al., 2005 ; Liu et al., 2008 ; Gao et al., 2009 ; Egusa and Abe, 2012 ).

Long-period stacking order precipitates that can exist at the grain boundaries, as well as intragranularly, are classified into two types, one that forms during solidification, and the other upon annealing ( Kawamura and Yamasaki, 2007 ; Li et al., 2018 ; Sato et al., 2018 ). It should be noted that, alloy composition permitting, the entire grains are composed of lamella of LPSO together with bands of α-Mg, while LPSO precipitates along the grain boundaries can also be present. Thus, the material, due to formation of LPSO structures, carries many FCC layers in each grain ( Kim et al., 2016 ). Building blocks of LPSO phases should be envisaged as SFs located between Shockley partial dislocations of α-Mg phase ( Zhu et al., 2009 , 2010a , b ; Kim et al., 2016 , 2017 ).

The classification of the crystal repetition of such layered structures goes back to the earlier work by Ramsdell (1947) . In earlier classification of LPSO phases, the 10H ( Matsuda et al., 2005 ; Abe et al., 2011 ; Hagihara et al., 2016 ), 18R ( Kawamura et al., 2006 ), 14H ( Itoi et al., 2004 ; Hagihara et al., 2010b ; Abe et al., 2011 ; Egusa and Abe, 2012 ; Zhu Y. M. et al., 2012 ; Jin et al., 2013 ; Nie et al., 2014 ), and 24R ( Abe et al., 2011 ) polytypes emerged, corresponding to 5, 6, 7, and 8 layers in structural blocks, each being a close-packed plane stacked in the direction of the c-axis of α-Mg crystal. Recently, an extended series have been expressed ( Li et al., 2018 ) as 6H (now known as a building block of 18R) ( Abe et al., 2002 ; Ping et al., 2002 ; Amiya et al., 2003 ), 10H, 14H, 15R ( Mi and Jin, 2013 ), 18R, and 24R. Some metastable LPSO phases were also revealed by the work of Kim et al. (2016) . In this notation, H stands for hexagonal, and R for rhombohedral symmetries of the Bravais systems, whereas the number refers to the number of repetitions of the structural blocks (SB) ( Kim et al., 2016 ), each of which essentially may also be seen as having HCP stacking involving SFs. The 4 polytypes can essentially be described by a structural unit composed of AB stacking followed by a C fault layer. This fault layer is enriched in Zn and RE atoms ( Egusa and Abe, 2012 ; Kim et al., 2017 ). Thus, the final ordered stacking, including the fault layer, makes up a local FCC, that is, ABCA stacking, and also shows chemical ordering perpendicular to the fault, that is, basal planes in α-Mg. As such, the workings of the system are reminiscent of Suzuki segregation and ordered segregation of the solute elements to twin boundaries as previously discussed.

The precise deciphering of the stacking sequences in 4 major types of LPSO phases in materials prepared via rapid solidification techniques has been given by Matsuda et al. (2005) and Egusa and Abe (2012) as follows: The 10H and 14H, both carrying mirror symmetry with respect to the basal plane, show stacking sequence of ABACBCBCAB and ACBCBABABABCBC, respectively. 18R and 24R, not carrying mirror symmetry with respect to the basal plane, have stacking sequence of ABABABCACACABCBCBC and ABABABABCACACACABCBCBCBC, respectively. It has been shown that 18R and 14H are stable at high and low temperatures, respectively, whereas 10H and 24R phases are not stable in every alloy system ( Kim et al., 2018a ). Furthermore, 14H and 18R are the most frequently observed ones ( Lv et al., 2014 ), with the 18R showing a tendency to transform into 14H upon heat treatment or hot deformation ( Oñorbe et al., 2012 ; Zhu Y. M. et al., 2012 ), as 14H appears to be energetically preferable one among the others ( Kim et al., 2016 ). This transformation from 18R to 14H was reported to be accompanied by a decrease in SFE ( Fan et al., 2011 ; Lv et al., 2014 ; Kim et al., 2016 ).

Long-period stacking order phases are further complicated by in-plane ordering in 14H and 18R types ( Kishida et al., 2015 ; Kim et al., 2018b ). This complication manifests itself with the presence of L1 2 type clusters, and the order is violated in one dimension, leading to the definition of order-disordered crystallographic structure in some Mg–TM-RE alloys ( Yokobayashi et al., 2011a ; Okamoto et al., 2014 ; Iwatake et al., 2015 ; Kishida et al., 2015 , 2017 ). The in-plane order may be a long-range type as in Mg–Al–Gd system ( Kimizuka et al., 2013 ; Tane et al., 2015 ; Kim et al., 2018b ) or may be composition dependent as in Mg–Y–Zn system, being present more locally in relatively dilute alloys, and long-range type in richer Mg–Y–Zn alloys ( Egusa and Abe, 2012 ). It has been suggested that LPSO formation is essentially governed by formation of Zn6RE8 clusters, with Mg atoms being substitutes for RE atoms ( Egusa and Abe, 2012 ). This in-plane ordered clusters were reported to have an important effect in determining the elastic properties of the LPSO structure and, in turn, influence the properties of the alloy ( Kimizuka et al., 2013 ; Tane et al., 2015 ; Kim et al., 2018b ). Another important effect of LPSO phases is inhibition of the dynamic recrystallization toward maintaining small grain size. This has been attributed to the suppression of dislocation numbers due to creation of many SFs on the basal planes ( Lv et al., 2014 ). 14H LPSO has been reported to be more effective in this regard as compared to 18R ( Lv et al., 2014 ).

The formation and growth mechanism of LPSO structures were investigated incorporating ab initio calculations ( Zhu Y. M. et al., 2012 ; Kim et al., 2016 ). Kim et al. (2017) suggested a coupled diffusional and displacive transformation mechanism involving formation of GP zones and their transformation to LPSO structures as opposed to the formerly proposed spinodal decomposition model ( Iikubo et al., 2013 ; Narita et al., 2013 ). According to their model, a Zn/Y-enriched layer was defined as the precursor of LPSO structure in lean Mg–Y–Zn system and termed as GP zones. Indeed, the term fits well as these zones fulfill the criteria of being chemically ordered and coherent with the matrix. At the stage of GP zones, it was shown that no stacking alterations in the HCP arrangement of the basal planes of α-Mg took place ( Kim et al., 2017 ). This primary step constituted the diffusional part of their suggested “coupled diffusional-displacive transformation” mechanism. In the following displacive step, LPSO structure is formed by generation and propagation of Shockley partials. Although in the original model the coherency strains were not mentioned explicitly, one can assume that the existence of such strains at precipitate–matrix interface, as in conventional GP zones, is inherent and facilitating the process. Formation of GP zones lowers the SFE paving the way for the formation of Shockley partials, at which stage the coherency stresses are substituted by the shear strains due to the partial dislocations ( Kim et al., 2016 ). Different types of these GP zones were said to lead to different LPSO structures, in terms of both chemical and structural ordering, and to be composition dependent ( Kim et al., 2017 ). Several other studies also reported GP zones in Mg alloys ( Ping et al., 2003 ; Oh et al., 2005 ; Nishijima et al., 2007 ; Saito et al., 2010 ; Lee et al., 2011 ).

Quasi-Crystal Forming Systems

Formation of quasi-crystals in Mg alloys may be viewed as an extension of the assessment of the potential for intermetallics through Miedema's scheme.

Quasi-crystals were discovered by Shechtman et al. (1984) in a rapidly solidified Al–manganese alloy. This discovery in 1984 was later awarded with Nobel Prize in 2011. Since then, other systems also have been found to exhibit quasi-crystal formations.

Quasi-crystals are essentially topologically closely packed intermetallics, also known as Frank–Kasper phases. Thermodynamically stable ( Abe et al., 2000 ) icosahedral (i-) ( Kounis et al., 2000 ) and decagonal (d-) phases were obtained. However, they are different from the true topologically close pack structures as they do not comply with the space-filling Bravais lattices. Instead, they possess a long-range quasi-periodic order without the translational periodicity in three dimensions, showing forbidden rotational symmetry in diffraction, that is, 5-, 10-fold, and so on.

The first quasi-crystal forming Mg system, Mg–Zn–(Y, RE), was reported by Luo et al. (1993) . It is now known that Mg–Zn–Al, Mg–Al–Cu/Ag/Au, Mg–Al– Zn–Cu, Mg–Al–Pd, and Mg–Cd–Yb alloy systems can form quasi-crystal phases ( Yadav and Mukhopadhyay, 2018 ). Quasi-crystalline phases themselves have interestingly low frictional properties, high hardness and oxidation resistance, low thermal conductivity, and so on ( Dubois, 2012 ).

It is interesting to note that once again Mg–TM–RE system, as for LPSO structures, is at the forefront in the case of quasi-crystal forming alloys. The icosahedral i -phase was obtained in Mg–Zn–Y system through normal casting conditions. Formation of quasi-crystalline phases in this system has been said to exhibit a relatively large compositional range, as well as casting process parameters ( Zhang et al., 2008 ). Zhao and Wang (2016) reported quasi-crystalline formations with 22 kinds of different morphologies obtained through different cooling processes in Mg–Zn–Y system. High strength values up to 450 MPa were reported for this system ( Bae et al., 2001 ).

An important outcome of their properties is that, because of their low interfacial energy, quasi-crystals are stable strengthening particles in Mg alloys ( Bae et al., 2002 ). Therefore, we may expect to see an increasing trend in their use.

A Competitor to Rare Earth Elements? Calcium Containing Alloys

The effect of Ca in Mg is similar to REs according to Miedema's model. Benefit of Ca may be summarized as follows: reduces the tension/compression asymmetry, refines grain size ( Jiang et al., 2015 ), increases creep resistance ( Ninomiya et al., 1995 ; Terada et al., 2005 ; Amberger et al., 2009 ), and reduces stress relaxation ( Abaspour et al., 2016 ) and deformation texture ( Stanford, 2010 ; Wang T. et al., 2014 ). An important issue is that all these benefits of Ca addition work in AM and AZ series commercial alloys. By combined addition of Ca and Sr, some commercial alloys were also developed such as ACX or AXJ series ( Suzuki et al., 2004 , 2008 ; Luo et al., 2007 ; Zhu et al., 2015 ).

Reported ab initio calculations of GSFE due to Ca addition are again not in unison as expressed before. For example, according to the majority of the literature ( Wang et al., 2013 ; Shang et al., 2014 ; Zhang et al., 2014 ; Yuasa et al., 2015 ; Dong et al., 2018 ), Ca decreased γ USF of Mg. Yet, in one study ( Moitra et al., 2014 ), Ca increased the GSFE basal of Mg (γ USF ) in <11 2 ¯ 0> slip indicating a strengthening effect equal to that of Gd, while Ce reducing it as RE elements. Whereas for another slip direction in basal plane, although lowering the SFE of pure Mg (γ SF ) and allowing for formation of an SF, Ca is more prohibitive as compared to Gd and Ce, for dislocation dissociation with much higher GSFE basal in <10 1 ¯ 0> slip. Reported trends were in better agreement on the effect of Ca in lowering the GSFE prismatic of Mg (γ USF ) in the {10 1 ¯ 0} <11 2 ¯ 0> slip system, being almost equal to those of Gd and Ce, indicating facilitation of dislocation generation. As to the pyramidal slip, Zhang et al. (2014) reported a decrease in GSFE of {11 2 ¯ 2} <11 2 ¯ 3> due to Ca, Gd, and Y to varying degrees.

From the above given account based on GSFE values, Ca falls no short of RE elements. The solid solution effect of Ca may also be viewed from the perspective of SRO effects. Calcium with its low electronegativity difference with Mg is likely to form a type of SRO similar to that in Mg–Y(RE), that is, hybridized bonds. Such elements are evidently more potent in improving the strength ( Abaspour et al., 2016 ).

When added to AZ series, it was said that Ca in the Mg 17 Al 12 eutectic phase increased the melting temperature of this otherwise insufficient-for-creep-strength phase, enhancing the strength of the Mg–Al bond ( Min, 2003 ). Depending on Al/Ca ratio, Ca addition also leads to formation of Laves phases, namely, Al 2 Ca, Mg 2 Ca, and (Mg, Al) 2 Ca ( Chai et al., 2018 ; Zubair et al., 2019 ). Among the Mg17Al12-, Al2Ca-, Mg2Sn-, and Mg2Ca-type intermetallics, based on the calculated enthalpy of formation and binding energies, Al2Ca was found to be the most stable one ( Wang et al., 2016 ).

RE elements are expensive, and therefore, it is desirable to find alloy compositions that can perform at least to the same level as those involving REs. Calcium is the best economic alloying element that can compete with the good-for-all-illnesses-of-Mg, the RE elements, as it seems to provide remedies for a number of shortcomings and anomalies of Mg alloys ( Abaspour et al., 2016 ; Guan et al., 2019 ). Furthermore, it has been shown that Ca addition conferred arguably the most attractive property to Mg, that is, protection of the melt against atmospheric corrosion, eliminating the need for a protective gas cover ( Kim, 2011 ) during secondary melting. In fact, calcium oxide (CaO) addition for this purpose, as an easier, and if not more, equally successful metallurgical option, may further compel researchers to examine the effects of Ca in a wider spectrum of Mg alloys as CaO would open the way to Ca entry into the melts. Therefore, as one of the highlights of the past two decades, we will also scrutinize the topic of CaO addition next.

CaO Addition to Mg—Improvements in Melt Protection and Corrosion of Mg Alloys

CaO addition may just be taken as one of the most important advancements over the past two decades regarding melt protection and imparting corrosion resistance to the conventional Mg alloys. It was shown that CaO addition by 0.3–0.7 wt%, without changing the basic microstructure except for grain refinement, singlehandedly conferred perhaps the most attractive property to Mg and to its conventional alloys in the AZ series, that is, protection of the melt against burning ( Kim, 2011 ).

Figure 8 ( Rafiei et al., 2018 ) shows the surface of a cast Mg without any protection during melting. Without CaO addition, a severe burning and oxidation would be imminent within a matter of seconds, now resulted in a surface with silvery metallic shine, as was observed in a number of AZ series alloys ( Kim, 2011 ). This ecologically friendly metallurgical practice, as emphasized by the foremost proponent of this method, Kim (2011) , further encompasses many other additional benefits, for example, metal cleanliness, grain refinement, and, consequently, improved mechanical properties and recyclability. The outcomes of CaO addition are expected to be particularly beneficial for the wrought Mg alloys, for which the processing route starts with billet or ingot castings ( Kim et al., 2007 ).

Figure 8 . Photomicrograph showing the effect of CaO addition on melt protection. Silvery surface shine of a cast Mg-0.4Al-1CaO (wt%) alloy piece solidified without protective gas (reproduced with permission from Rafiei et al., 2018 ; https://www.civilica.com/Paper-IMES12-IMES12_010.html ).

Exploration of the possibility of using CaO addition can be traced back to the preceding work by Sakamoto et al. (1997) , reporting that Ca in pure Mg was increasing the flammability resistance. However, handling Ca industrially is a difficult and expensive operation. Moreover, Ca addition as a means for melt protection, although successful, has been reported to alter both the material properties, as well as the processing parameters employed, whereas CaO was doing the same job equally well arguably without releasing substitutional Ca into the solid solution ( Kim, 2011 ; Lee and Kim, 2011a ). Other already foreseen difficulties in Ca addition were mentioned as decreased in metal fluidity, increased die sticking, and problems related to utilization of Ca-containing scrap ( Kim, 2011 ; Lee and Kim, 2011b ).

The initial addition of CaO to Mg melt is a rather slow process, during which melt protection using a protective gas cover would still be needed ( Kim et al., 2007 ; Lee and Kim, 2011a , b ). Once added, otherwise an insufficient N 2 gas cover ( Holtzer and Bobrowski, 2008 ) was claimed to do the job effectively in the secondary melting operations.

Initially, there was a contradiction, not on the outcomes of CaO addition but as to what happens to CaO in molten metal. First, CaO was supposed to be more stable than MgO according to Ellingham diagrams ( Brain and Knacke, 1973 ). Second, in some reports, it was stated that CaO dispersed in pure Mg and AZ series alloys ( Huang et al., 2004 ; Ha et al., 2008 ; Kondoh et al., 2011 ; Nam et al., 2012 ). It was also claimed that CaO was not to survive during solidification but to transform into Mg 2 Ca phase in pure Mg ( Ha et al., 2006 ) and into Al 2 Ca, and/or (Mg,Al) 2 Ca, if added to AZ series ( Kim, 2011 ; Lee and Kim, 2011b ). The first issue was resolved by a thermodynamic analysis, showing the possibility of CaO dissociation against the formation of Mg 2 Ca Laves phase ( Kondoh et al., 2011 ). The second issue, via a TEM study on AZ31 ( Jeong et al., 2013 ), was also resolved, showing that survival of CaO particles could be attributed to the solidification rate and that the difference between Ca and CaO additions lies in the agglomeration tendency of the intermetallics in CaO-added cases. A following in situ study ( Wiese et al., 2015 ) also confirmed CaO dissolution that even started in solid state and increased until melting.

CaO addition was also proven useful in increasing the ignition temperatures of pure Mg and AZ series alloys, lessening concerns about safe handling of machining chips ( You et al., 2000 ; Lee and Kim, 2009a , b , 2011b ; Kim, 2011 ), as well as paving the way for use in aviation applications. An earlier study also reported this improvement in Ca-added Mg. Although the ignition temperature decreases with increasing Al content with a corresponding decrease in melting temperatures for AZ alloys, it was shown that CaO addition in all AZ series, MRI153, MRI230, and AS21 alloys, led to increasing ignition temperatures. A noteworthy example was the remarkable figure of 1,177°C for AZ31 with 1.22 wt% CaO ( Kim, 2011 ). In addition to the flammability findings, general corrosion resistance of Mg and AZ series alloys was also reported to have benefited greatly from the addition of CaO ( You et al., 2000 ; Lee and Kim, 2009a , b ; Kim, 2011 ). The conclusion arrived was that the Al content had an adverse effect, and the total amount of Ca-bearing phases was the determining figure for the ignition temperature ( Lee and Kim, 2011b ).

The oxide film forming on the CaO-added Mg and Mg alloys was said not to conform to the Pilling–Bedworth ( Pilling and Bedworth, 1923 ) theory that requires no volumetric change between the unit metal and the oxide phase replacing it for formation of a protective oxide film. According to the Pilling–Bedworth theory, pure Mg forms an unprotective MgO as the related R value is less than unity, being only 0.83, whereas CaO has even a worse figure of 0.78. It appears that these figures, as they may not represent the case for a mixed oxide, are counterintuitive to explain the improvement in the case CaO addition. Although a dense oxide film formation ( Lee and Kim, 2011b ) was assumed to explain the protective effect of CaO addition, the nature of this phenomenon in terms of structure of the surface oxide requires further exploration.

It is fair to say that much work is still needed to understand whether such use of CaO is universally applicable for all, and especially for the potentially useful novel Mg alloys of the future, and in terms of suitability to different popular production methods. For example, a twin-roll-casting study ( Li et al., 2010 ) showed that both Al and Ca contents deteriorated the surface quality of the product in AZ series alloys. The fact that Ca-containing complex intermetallics were found in CaO-added structures should also be taken to indicate this necessity for a more comprehensive research on alloys involving elements having the potential to form precipitates with Ca.

Conclusions and Suggestions for Future Work

Stacking fault energy changes due to addition of solute atoms into a host system are not straightforward to understand. On the other hand, Miedema's model leads to a better understanding of the free electron density distribution and the consequent SFE changes presented by the ab initio calculations. The fundamental terms of the atomic-level thermodynamic expression given by Miedema, that is, n WS (density of electrons at the boundary of the two atomic cells, Wigner–Seitz cells) and Φ * (the difference in chemical potential for electrons or equivalently the difference in electronegativity, or difference between the work functions), have been shown to be related to SFE in binary systems.

The qualitative relationship of those terms in Miedema's model with SFE shows that the employment of work function measurements (e.g., Kelvin Probe Force Microscopy) is possible to, at least, qualitatively assess the influence of the extra alloying elements into an alloy system with reference to a pure or binary system. Thus, a qualitative assessment of the changes in SFE in multicomponent systems can be undertaken readily when experimentally developing new alloys. This point may be appreciated better when considering the fact that ab initio calculations in multicomponent systems are currently not feasible.

Furthermore, it seems reasonable to indicate the need to extend the atomic-level thermodynamic assessment according to Miedema's approach to multicomponent systems. This difficult task would then facilitate a more complete evaluation and allow predictions in terms of precipitate forming multicomponent alloy systems, especially in terms of those that form LPSO phases or quasi-crystals.

The concept of SRO indicates the possibility of designing dilute alloy systems with desirable engineering properties. This concept also indicates the possibility to alter the freezing range of alloys with dilute additions; that is, strong SRO may expand the freezing range, as a critical parameter for casting operations such as twin roll casting. There appears to be sufficient literature that warrants further studies to explore the types of SRO through first-principles calculations, which include DOS computations. Our evaluation of the existing literature has indicated that two types of SRO can be expected depending on whether hybridization occurs in electron sharing between neighboring atoms. Miedema's geometric scheme also shows such categorization for binary alloys of Mg in terms of upper (north) and lower (south) sectors in a plot of n WS vs. Φ * .

The case of dilute levels of oxygen in Mg, or in other metals, presents a particularly interesting example in this regard. Presence of trace amounts of oxygen in different Mg alloy systems deserves attention.

The highly useful addition of Ca/CaO needs to be examined in a broader perspective in terms of its melt protection and the probable concomitant precipitation effects, as well as influences on castability or other processing techniques.

It should be indicated that some Mg alloy systems, such as those involving LPSO phases or quasi-crystals, and those containing Ca or dilute amount of oxygen have been developed, which offer superior engineering properties and solutions to the relatively problematic features of Mg. A steady increase in the use of Mg alloys can therefore be expected.

Author Contributions

The author confirms being the sole contributor of this work and has approved it for publication.

Conflict of Interest

The author declares that the research was conducted in the absence of any commercial or financial relationships that could be construed as a potential conflict of interest.

Acknowledgments

I would like to thank to my students Sevcan Arslan, Talha Cakmak, and Ugurcan Ozogut for their help in preparation of the figures. I also extend my special thanks to my friend Prof. Dr. Ahmet Oral of Middle East Technical University for conducting the KPFM measurements at Nanomagnetics Instruments Co. The author also thankfully acknowledges the financial support provided by Scientific Research Projects (BAP) office of Mugla Sitki Kocman University toward the production of microscopy and KPFM work within the Project no: 16/070.

Abaspour, S. (2014). Thermodynamics-based design of creep resistant mg solid solutions using the miedema scheme (Ph.D. thesis). Queensland: The University of Queensland, Australia.

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Keywords: magnesium alloys, doping of magnesium, dilute alloys, short range order, LPSO phases, rare earth alloys, RE-free magnesium alloys

Citation: Kaya AA (2020) A Review on Developments in Magnesium Alloys. Front. Mater. 7:198. doi: 10.3389/fmats.2020.00198

Received: 02 August 2019; Accepted: 26 May 2020; Published: 17 August 2020.

Reviewed by:

Copyright © 2020 Kaya. This is an open-access article distributed under the terms of the Creative Commons Attribution License (CC BY) . The use, distribution or reproduction in other forums is permitted, provided the original author(s) and the copyright owner(s) are credited and that the original publication in this journal is cited, in accordance with accepted academic practice. No use, distribution or reproduction is permitted which does not comply with these terms.

*Correspondence: A. Arslan Kaya, aakaya@mu.edu.tr

Disclaimer: All claims expressed in this article are solely those of the authors and do not necessarily represent those of their affiliated organizations, or those of the publisher, the editors and the reviewers. Any product that may be evaluated in this article or claim that may be made by its manufacturer is not guaranteed or endorsed by the publisher.

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Significance of alloying elements on the mechanical characteristics of mg-based materials for biomedical applications.

1. Introduction

2. alloying elements suitable for biomedical application, 2.1. calcium (ca), 2.2. aluminum (al), 2.3. copper (cu), 2.4. manganese (mn), 2.5. bismuth (bi), 2.6. iron (fe), 2.7. lithium (li), 2.8. molybdenum (mo), 2.9. holmium (ho), 2.10. erbium (er), 2.11. gadolinium (gd), 2.12. cerium (ce), 2.13. lanthanum (la), 2.14. neodymium (nd), 2.15. strontium (sr), 2.16. zirconium (zr), 2.17. yttrium (y), 2.18. silver (ag), 2.19. tin (sn), 2.20. zinc (zn), 3. classification of mg alloy and influence of alloying element on various mg alloys, 3.1. mg-al based alloys, 3.1.1. az alloy series, 3.1.2. am alloy series, 3.2. mg-zn based alloys, 3.2.1. mg-zn-ca alloys, 3.2.2. mg-zn-mn alloys, 3.2.3. mg-zn-re-based alloys, 3.3. mg-ca alloy, 3.4. mg-re alloy, mg-re-zn alloys, 3.5. we system alloys, 3.6. mg-li alloys, 4. conclusions, outlooks, and future aspects, author contributions, institutional review board statement, informed consent statement, data availability statement, conflicts of interest.

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Sharma, S.K.; Saxena, K.K.; Malik, V.; Mohammed, K.A.; Prakash, C.; Buddhi, D.; Dixit, S. Significance of Alloying Elements on the Mechanical Characteristics of Mg-Based Materials for Biomedical Applications. Crystals 2022 , 12 , 1138. https://doi.org/10.3390/cryst12081138

Sharma SK, Saxena KK, Malik V, Mohammed KA, Prakash C, Buddhi D, Dixit S. Significance of Alloying Elements on the Mechanical Characteristics of Mg-Based Materials for Biomedical Applications. Crystals . 2022; 12(8):1138. https://doi.org/10.3390/cryst12081138

Sharma, Sachin Kumar, Kuldeep Kumar Saxena, Vinayak Malik, Kahtan A. Mohammed, Chander Prakash, Dharam Buddhi, and Saurav Dixit. 2022. "Significance of Alloying Elements on the Mechanical Characteristics of Mg-Based Materials for Biomedical Applications" Crystals 12, no. 8: 1138. https://doi.org/10.3390/cryst12081138

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Research and Development in Magnesium Alloys for Industrial and Biomedical Applications: A Review

• Published: 19 July 2019
• Volume 26 , pages 409–430, ( 2020 )

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• Vaira Vignesh Ramalingam 1 ,
• Padmanaban Ramasamy   ORCID: orcid.org/0000-0002-4605-646X 1 ,
• Mohan Das Kovukkal 1 &
• Govindaraju Myilsamy 1  

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173 Citations

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The work reviews the research and development status of magnesium alloy, with more attention to the methodologies and technologies adopted to improve the properties of AZ91 alloy. The drive force of utilizing magnesium alloys for automotive and biomedical application is light weightiness and biocompatibility respectively. However, the softness and high activity of magnesium alloys result in high wear and high corrosion rate respectively. One of the essential factors influencing the properties of magnesium alloy is its microstructure. Consequently, the grain size, morphology and distribution of phase constituents influence the properties of magnesium alloys. The modification of microstructure through processing route (hot working and cold working), heat treatment, and alloying elements improves the mechanical, corrosion, biocompatible, and tribological properties of magnesium alloys. Besides microstructural modification processes, addition of reinforcements, and coatings improves the properties of magnesium alloys. This article emphasis on the recent research on the technologies to improve the microstructure, hardness, tensile strength, ductility, yield strength, wear resistance, and corrosion resistance of magnesium alloy AZ91. Moreover, this review addresses the key issues hindering the applications of magnesium alloys for structural and biomedical applications.

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Vaira Vignesh Ramalingam, Padmanaban Ramasamy, Mohan Das Kovukkal & Govindaraju Myilsamy

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Ramalingam, V.V., Ramasamy, P., Kovukkal, M.D. et al. Research and Development in Magnesium Alloys for Industrial and Biomedical Applications: A Review. Met. Mater. Int. 26 , 409–430 (2020). https://doi.org/10.1007/s12540-019-00346-8

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DOI : https://doi.org/10.1007/s12540-019-00346-8

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Journal of Materials Chemistry B

Effects of alloying elements on the corrosion behavior and biocompatibility of biodegradable magnesium alloys: a review.

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a Institute for Frontier Materials, Deakin University, Geelong, Victoria 3217, Australia E-mail: [email protected] Fax: +61 352271103 Tel: +61 352272168

b Faculty of Science, Engineering and Technology, Swinburne University of Technology, Hawthorn, Victoria 3122, Australia

Magnesium (Mg) based alloys have been extensively considered for their use as biodegradable implant materials. However, controlling their corrosion rate in the physiological environment of the human body is still a significant challenge. One of the most effective approaches to address this challenge is to carefully select alloying compositions with enhanced corrosion resistance and mechanical properties when designing the Mg alloys. This paper comprehensively reviews research progress on the development of Mg alloys as biodegradable implant materials, highlighting the effects of alloying elements including aluminum (Al), calcium (Ca), lithium (Li), manganese (Mn), zinc (Zn), zirconium (Zr), strontium (Sr) and rare earth elements (REEs) on the corrosion resistance and biocompatibility of Mg alloys, from the viewpoint of the design and utilization of Mg biomaterials. The REEs covered in this review include cerium (Ce), erbium (Er), lanthanum (La), gadolinium (Gd), neodymium (Nd) and yttrium (Y). The effects of alloying elements on the microstructure, corrosion behavior and biocompatibility of Mg alloys have been critically summarized based on specific aspects of the physiological environment, namely the electrochemical effect and the biological behavior.

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Y. Ding, C. Wen, P. Hodgson and Y. Li, J. Mater. Chem. B , 2014,  2 , 1912 DOI: 10.1039/C3TB21746A

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Novel insights on different treatment of magnesium alloys: A critical review

Affiliations.

• 1 Department of Mechanical Engineering, KPR Institute of Engineering and Technology, Coimbatore, India.
• 2 Department of Mechanical Engineering, Institute of Technology, Hawassa University, Ethiopia.
• 3 School of Mechanical and Automotive Engineering, Qingdao University of Technology, Qingdao, 266520, China.
• 4 Mechanical Engineering Department, University Center for Research and Development, Chandigarh University, Mohali, 140413, Punjab, India.
• 5 Department of Automobile Engineering, Chandigarh University, Mohali, 140413, Punjab, India.
• 6 Future University in Egypt, New Cairo, 11835, Egypt.
• 7 Poznan University of Technology, Poznan, 60-965, Poland.
• PMID: 36439742
• PMCID: PMC9694116
• DOI: 10.1016/j.heliyon.2022.e11712

Magnesium alloys are extensively used for weight reduction in automotive and aircraft applications. This research presents the effect of heat and cryogenic treatment on aluminium-zinc-based Mg alloys. Both treatments can improve the mechanical and corrosion properties of the AZ series Mg alloy. The review deals with a broad understanding of the microstructure changes that occur during heat and cryogenic treatment of Mg alloy. The mechanical and corrosion characteristics of heat and cryogenic treated AZ31, AZ91, AZ63, and AZ80 Mg alloys are discussed. The essential strengthening mechanisms of heat and cryogenic treated AZ series Mg are discussed with microstructure changes. This review has also shown a few gaps in research on the selection of suitable pre- and post-treatment processes for Mg alloy. The effects on grain refinement and the formation of secondary phase particles are discussed in detail. The related crystallographic plane, twining, and dislocation changes are out of the scope of this review. Finally, the correlations of the above changes to mechanical properties are the directions of the future.

Keywords: Corrosion resistance; Heat treatment; Magnesium alloys; Microstructure; Tensile strength.

© 2022 The Authors.

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Conflict of interest statement

The authors declare no conflict of interest.

Applications of Mg alloy.

Microstrcutre of Cast AZ31B Mg…

Microstrcutre of Cast AZ31B Mg alloy (a) before heat treatment (b) after heat…

Microstrcture (a) before cryogenic treatement…

Microstrcture (a) before cryogenic treatement (b) after crygenic treatment.

Microstructure of heat treated AZ63…

Microstructure of heat treated AZ63 Mg alloy.

Microstructure of heat treated cast…

Microstructure of heat treated cast AZ91 Mg alloy.

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