Effect of Transition Metal Elements on High-Temperature Properties of Al–Si–Cu–Mg Alloys

In the present work, we studied the effects of transition metal elements on microstructure evolution and high-temperature mechanical properties via the preparation of new modified alloys with micro-additions of Cr, Ti, V, Zr, Mo, and Mn to address the poor high-temperature performance of Al–Si–Cu–Mg alloys for automotive engines. The results show that the addition of transition metal elements formed a variety of new intermetallic phases that were stable at high temperatures, such as (AlSi)3(TiVZr), (AlSi)3Ti, (AlSi)3(CrVTi), Al74Si6Mn4Cr2Fe, Al85Si5Mn2Mo2CrFe, Al0.78Fe4.8Mn0.27Mo4.15Si2, (AlSi)2(CrVTi)Mo, and Al13(MoCrVTi)4Si4, and these phases evidently improved the ultimate high-temperature tensile strength and yield strength. The ultimate tensile strength and yield strength of the modified alloy increased by 17.49% and 31.65% when the test temperature increased to 240 °C, respectively, and by 71.28% and 74.73% when the test temperature increased to 300 °C, respectively. The fundamental reason for this change is that the intermetallic phase hinders the expansion of cracks, which can exist stably at high temperatures. When a crack extends to the intermetallic phases, it will break along with the intermetallic phases or propagate along the morphological edge of the intermetallic phases.


Introduction
Al-Si casting alloys are widely used in manufacturing automotive engine cylinder heads due to their advantages of being lightweight, good casting performance, and excellent comprehensive mechanical properties [1]; however, with the contradictory development of high load stress and thin-walled structure of the high-performance engine, the requirements for the balance of strength and toughness at room temperature as well as the high-temperature performance of aluminum alloy cylinder heads and engine blocks are becoming stricter. To meet this market demand, researchers began to study how to achieve better values of both strength and ductility at room temperature and improve the high-temperature performance of Al-Si casting alloys. Li Runxia et al. [2] found that Al-Si alloy's strength and toughness can be improved by adjusting the content of Cu and Mg. According to the literature [3][4][5], adjusting the Cu/Mg ratio changed the formation process of strengthening phases in Mg 2 Si, Q-Al 5 Mg 8 Si 4 Cu 2 , and θ-Al 2 Cu, and thus changed the strength and toughness of the alloy; however, the traditional intermetallic phase such as Mg 2 Si, Q-Al 5 Mg 8 Si 4 Cu 2 , and θ-Al 2 Cu phase will coarsen rapidly above 200 • C [6]; therefore, the strengthening effect by these intermetallic phases can remain only at room temperature. To keep the microstructure of the aluminum alloy cylinder head stable and strong at temperatures higher than 200 • C, it is necessary to find micro-alloy elements that can form a thermally stable strengthening phase with the main alloy elements (Al-Si-Cu-Mg) and make the alloy stronger and tougher simultaneously. In recent years, the elements that meet the above conditions are Cr, Ti, V, Zr, Mo, Mn, and other transition metal elements.

Materials and Methods
The experimental alloys were prepared in a graphite crucible resistance furnace by melting commercial master alloys of Al-20Si, Al-40Cu, Al-5Ti-B, Al-10Sr, Al-20Cr, Al-6Ti, Al-20V, Al-10Zr, Al-6Mo, and Al-10Mn in wt% and pure Al, Mg, and Zn metals to achieve the selected alloy chemistry, as listed in Table 1. The base alloy without the transition metal element is named BA, and the alloy with the transition metal-element is named MA. After casting, the test bar was heat treated. The test bars were divided into two groups: one group was heat treated with the solid solution treatment; the other group was heat treated with the aging treatment after the solution treatment. The solution temperature of the test bars with only the solution treatment was set to 500, 520, 540, and 560 • C. The heat treatment process for the other test bars was applying the solution treatment at 500 • C for 4 h and 520 • C for 5 h, followed by quenching in water at 60 • C, then applying aging treatment at 90 • C for 3 h and at 180 • C for 6 h. All test bars were processed and formed according to GB/T 6397-86 (Chinese Standard for Metal tensile test specimen) Metallic materials-Test pieces for tensile testing, as shown in Figure 1. After processing, the tensile test was carried out on the test bars. The corresponding relationship between heat treatment and tensile test temperature is shown in Table 2. The high temperature tensile test was carried out on electronic universal testing machine (DDL100, Changchun Institute of Mechanical Science Co., Ltd, Changchun, China), with the test temperature of 25, 80, 160, 240, and 300 • C, and the tensile speed of 2 mm/min. Before the tensile test, the bars were heated to the test temperature in the heating chamber at a speed of 10 • C/min, and kept for 10 min. After stretching, the specimen was cut off 2 mm below the fracture surface by electrical discharge machining, polished and etched with Keller reagent (5 mL HNO3 + 3 mL HCL + 2 mL HF + 190 mL deionized water), and then carried out with Leica (DM2700M, Leica microsystems Co., Ltd, Wetzlar, Germany) optical microscope equipped with ISA4 metallographic image quantitative analysis system and Zeiss (SUPRA55, CarlZeiss AG, Oberkochen, Germany) scanning electron microscope equipped with Energy Disperse System. treatment and tensile test temperature is shown in Table 2. The high temperature tensile test was carried out on electronic universal testing machine (DDL100, Changchun Institute of Mechanical Science Co., Ltd, Changchun, China), with the test temperature of 25, 80, 160, 240, and 300 °C, and the tensile speed of 2 mm/min. Before the tensile test, the bars were heated to the test temperature in the heating chamber at a speed of 10 °C/min, and kept for 10 min. After stretching, the specimen was cut off 2 mm below the fracture surface by electrical discharge machining, polished and etched with Keller reagent (5 mL HNO3 + 3 mL HCL + 2 mL HF + 190 mL deionized water), and then carried out with Leica (DM2700M, Leica microsystems Co., Ltd, Wetzlar, Germany) optical microscope equipped with ISA4 metallographic image quantitative analysis system and Zeiss (SU-PRA55, CarlZeiss AG, Oberkochen, Germany) scanning electron microscope equipped with Energy Disperse System.

13#
Al38.  Figure 3 shows the XRD analysis of the BA and the MA added with the transition metal elements. The existence of α-Al and eutectic silicon was confirmed by comparing the diffraction peaks; the corresponding peaks are marked with squares and triangles, respectively. The diffraction peaks corresponding to the rich TiVZr phase, rich CrVTi phase, and rich MoMnFe phase were found through the amplification of the diffraction peaks, which were named (AlSi)x(TiVZr), (AlSi)x(CrVTi), and (AlSiMnFe)x(MoCr) phases, and the corresponding peaks were marked with a diamond, star, and pentagram, respectively. This result is consistent with the results determined by EDS and compared with the results determined by literature. However, due to the small amount of transition alloy elements, the diffraction peaks in XRD patterns are low, and because of the existence of some impurity peaks, it is difficult to distinguish the specific intermetallic phases. In order to characterize the failure mechanisms, electrical discharge machining was used to cut the bar parallel to the tensile axis to expose the center of the cylindrical bar, and ground and polished the cut surface. Through observation, four kinds of intermetallic phases were found in the fracture. These four kinds of intermetallic phases are  In order to characterize the failure mechanisms, electrical discharge machining was used to cut the bar parallel to the tensile axis to expose the center of the cylindrical bar, and ground and polished the cut surface. Through observation, four kinds of intermetallic phases were found in the fracture. These four kinds of intermetallic phases are  Figure 4c); however, the fracture of the (AlSi) 2 (CrVTi)Mo (17#) phase is different (Figure 4d). After the fracture of the test bar, the morphology of (AlSi) 2 (CrVTi)Mo (17#) phase is complete, and the fracture path is along the boundary of (AlSi) 2 (CrVTi)Mo (17#) phase. 21, 11, x FOR PEER REVIEW 6 of 12 fracture of the Al13(MoCrVTi)4Si4 (18#) phases occurs with the macro crack across the test bar ( Figure 4c); however, the fracture of the (AlSi)2(CrVTi)Mo (17#) phase is different (Figure 4d). After the fracture of the test bar, the morphology of (AlSi)2(CrVTi)Mo (17#) phase is complete, and the fracture path is along the boundary of (AlSi)2(CrVTi)Mo (17#) phase.

Alloy Tensile Properties
The tensile properties of the BA and MA, heat-treated at different solution temperatures of respectively 500, 520, 540, and 560 °C for 6 h, were tested at room temperature and are shown in Figure 5. The heat treatment process of the test bar used for testing here is the solution-only treatment. The results show that the UTS, YS, and percent elongation (%EL) all increase at first and then decrease with the increase in solution temperatures and reach the peak at 520 °C. It is worth noting that when the solution treatment temperature is higher than 520 °C, although the tensile properties of the two alloys tend to decline, the tensile properties of the BA decrease much faster than that of the MA at room temperature.

Alloy Tensile Properties
The tensile properties of the BA and MA, heat-treated at different solution temperatures of respectively 500, 520, 540, and 560 • C for 6 h, were tested at room temperature and are shown in Figure 5. The heat treatment process of the test bar used for testing here is the solution-only treatment. The results show that the UTS, YS, and percent elongation (%EL) all increase at first and then decrease with the increase in solution temperatures and reach the peak at 520 • C. It is worth noting that when the solution treatment temperature is higher than 520 • C, although the tensile properties of the two alloys tend to decline, the tensile properties of the BA decrease much faster than that of the MA at room temperature. fracture of the Al13(MoCrVTi)4Si4 (18#) phases occurs with the macro crack across the test bar ( Figure 4c); however, the fracture of the (AlSi)2(CrVTi)Mo (17#) phase is different (Figure 4d). After the fracture of the test bar, the morphology of (AlSi)2(CrVTi)Mo (17#) phase is complete, and the fracture path is along the boundary of (AlSi)2(CrVTi)Mo (17#) phase.

Alloy Tensile Properties
The tensile properties of the BA and MA, heat-treated at different solution temperatures of respectively 500, 520, 540, and 560 °C for 6 h, were tested at room temperature and are shown in Figure 5. The heat treatment process of the test bar used for testing here is the solution-only treatment. The results show that the UTS, YS, and percent elongation (%EL) all increase at first and then decrease with the increase in solution temperatures and reach the peak at 520 °C. It is worth noting that when the solution treatment temperature is higher than 520 °C, although the tensile properties of the two alloys tend to decline, the tensile properties of the BA decrease much faster than that of the MA at room temperature. Tensile tests were carried out at different temperatures (25, 80, 160, 240, and 300 °C) after the T6 heat treatment (solution and ageing heat treatment) of the two alloys, and the obtained data are shown in Figure 6. Obviously, with the increase in test temperature, the UTS and YS of the alloy show a decreasing trend, while the %EL of the alloy increases with the increase in temperature. It is worth mentioning that the strength values (UTS, YS) of the MA are better than those of the BA in all test temperature ranges (25-300 °C). In addition, the reduction response of the BA strength value significantly changed at 160 °C. Taking 160 °C as the critical temperature, the calculated change value of performance reduction response is shown in Table 4. Obviously, when the temperature is lower than 160 °C, the performance reduction response of the two alloys is almost the same. When the temperature is higher than 160 °C, the advantage of MA alloy is obvious.  Tensile tests were carried out at different temperatures (25, 80, 160, 240, and 300 • C) after the T6 heat treatment (solution and ageing heat treatment) of the two alloys, and the obtained data are shown in Figure 6. Obviously, with the increase in test temperature, the UTS and YS of the alloy show a decreasing trend, while the %EL of the alloy increases with the increase in temperature. It is worth mentioning that the strength values (UTS, YS) of the MA are better than those of the BA in all test temperature ranges (25-300 • C). In addition, the reduction response of the BA strength value significantly changed at 160 • C. Taking 160 • C as the critical temperature, the calculated change value of performance reduction response is shown in Table 4. Obviously, when the temperature is lower than 160 • C, the performance reduction response of the two alloys is almost the same. When the temperature is higher than 160 • C, the advantage of MA alloy is obvious. Tensile tests were carried out at different temperatures (25, 80, 160, 240, and 300 °C) after the T6 heat treatment (solution and ageing heat treatment) of the two alloys, and the obtained data are shown in Figure 6. Obviously, with the increase in test temperature, the UTS and YS of the alloy show a decreasing trend, while the %EL of the alloy increases with the increase in temperature. It is worth mentioning that the strength values (UTS, YS) of the MA are better than those of the BA in all test temperature ranges (25-300 °C). In addition, the reduction response of the BA strength value significantly changed at 160 °C. Taking 160 °C as the critical temperature, the calculated change value of performance reduction response is shown in Table 4. Obviously, when the temperature is lower than 160 °C, the performance reduction response of the two alloys is almost the same. When the temperature is higher than 160 °C, the advantage of MA alloy is obvious.   Compared to the BA, the UTS and YS of the MA are only increased by 1.36% and 3.44% at room temperature, 3.41% and 6.85% at 160 • C, 17.49%, and 31.65% at 240 • C respectively; when the temperature rises to 300 • C, the UTS and YS are increased by 71.28% and 74.73%, respectively.

Thermal Stability Analysis of Alloy Elements
SEM/EDS facial scanning was carried out to investigate the thermal stability of the intermetallic phases in the MA and to observe and judge whether the elements could remain in the aggregation state or whether the phenomenon of dissolution and homogenization occurred. The scanning object is the sample containing eight alloying elements Cu, Mg, V, Zr, Ti, Cr, Mn, and Mo, which were heat-treated at the solution temperature of 500, 520, 540, and 560 • C, respectively. The scanning results are shown in Figure 7. The Cu and Mg atomic groups have been partially dissolved at 500 • C for 6 h, whereas the Cu and Mg atoms are completely dissolved and homogenized when the temperature rises to 520 • C. The atomic groups of V, Zr, and Ti can keep aggregation at 520 • C, but when the temperature rises to 540 • C, the atomic groups of V, Zr, and Ti are dissolved and homogenized, and their thermal stability lost. Compared with the above-mentioned five elements, Cr, Mn, and Mo have better thermal stability, and the atomic groups of the three elements still do not dissolve and homogenize after being kept at 560 • C for 6 h, and can remain aggregated.  Compared to the BA, the UTS and YS of the MA are only increased by 1.36% and 3.44% at room temperature, 3.41% and 6.85% at 160 °C, 17.49%, and 31.65% at 240 °C respectively; when the temperature rises to 300 °C, the UTS and YS are increased by 71.28% and 74.73%, respectively.

Thermal Stability Analysis of Alloy Elements
SEM/EDS facial scanning was carried out to investigate the thermal stability of the intermetallic phases in the MA and to observe and judge whether the elements could remain in the aggregation state or whether the phenomenon of dissolution and homogenization occurred. The scanning object is the sample containing eight alloying elements Cu, Mg, V, Zr, Ti, Cr, Mn, and Mo, which were heat-treated at the solution temperature of 500, 520, 540, and 560 °C, respectively. The scanning results are shown in Figure 7. The Cu and Mg atomic groups have been partially dissolved at 500 °C for 6 h, whereas the Cu and Mg atoms are completely dissolved and homogenized when the temperature rises to 520 °C. The atomic groups of V, Zr, and Ti can keep aggregation at 520 °C, but when the temperature rises to 540 °C, the atomic groups of V, Zr, and Ti are dissolved and homogenized, and their thermal stability lost. Compared with the above-mentioned five elements, Cr, Mn, and Mo have better thermal stability, and the atomic groups of the three elements still do not dissolve and homogenize after being kept at 560 °C for 6 h, and can remain aggregated.

Discussion
In Section 3.3, it was observed that Cu and Mg atomic groups have been partially dissolved at 500 °C, whereas Cu and Mg atomic groups are completely dissolved and homogenized when the temperature is raised to 520 °C for 6 h. This result clearly shows that the thermal stability of the Cu-rich phase and the Mg-rich phase is poor, and it can also explain why the traditional Al-Si-Cu-Mg alloy has excellent properties at room temperature-its mechanical properties will greatly decrease when the temperature rises. In other words, it is precisely because the Cu and Mg atoms have been diffused and homogenized, and this phenomenon will inevitably lead to the dissolution of rich Cu phase and rich Mg phase, which cannot have a beneficial effect on the high-temperature properties of the alloy. These phases are mostly present in the traditional intermetallic phase, such as Al2Cu, Mg2Si, and Q-Al5Cu2Mg8Si6, which plays a strengthening role at room temperature. This shows that Cu and Mg atoms have adverse effects on the high-temperature stability of the intermetallic phase. In comparison, because V, Zr, and Ti atomic groups can keep aggregation at a higher temperature, the thermal stability of intermetallic phases rich V, Zr, and Ti must also be improved; Cr, Mn, and Mo atoms have higher thermal stability,

Discussion
In Section 3.3, it was observed that Cu and Mg atomic groups have been partially dissolved at 500 • C, whereas Cu and Mg atomic groups are completely dissolved and homogenized when the temperature is raised to 520 • C for 6 h. This result clearly shows that the thermal stability of the Cu-rich phase and the Mg-rich phase is poor, and it can also explain why the traditional Al-Si-Cu-Mg alloy has excellent properties at room temperature-its mechanical properties will greatly decrease when the temperature rises. In other words, it is precisely because the Cu and Mg atoms have been diffused and homogenized, and this phenomenon will inevitably lead to the dissolution of rich Cu phase and rich Mg phase, which cannot have a beneficial effect on the high-temperature properties of the alloy. These phases are mostly present in the traditional intermetallic phase, such as Al 2 Cu, Mg 2 Si, and Q-Al 5 Cu 2 Mg 8 Si 6 , which plays a strengthening role at room temperature. This shows that Cu and Mg atoms have adverse effects on the high-temperature stability of the intermetallic phase. In comparison, because V, Zr, and Ti atomic groups can keep aggregation at a higher temperature, the thermal stability of intermetallic phases rich V, Zr, and Ti must also be improved; Cr, Mn, and Mo atoms have higher thermal stability, without dissolution, even at 560 • C. It can be inferred that the thermal stability of the new intermetallic phases should be higher than that of the traditional intermetallic phases due to the presence of V, Zr, Ti, Cr, Mn, and Mo atoms, especially Cr, Mn, and Mo atoms.
During the microstructure analysis, it was found that V, Zr, and Ti atoms mainly exist in the rich TiVZr phase, whereas Cr, Mn, and Mo atoms are mainly distributed in the rich CrVTi phase, rich TiVMo phase, and rich MoMnFe phase. It was found that the rich TiVZr phase will lose its thermal stability when working at 540 • C or above, whereas the rich CrVTi phase, rich TiVMo phase, and rich MoMnFe phase cannot dissolve and homogenize under the working conditions of ≤580 • C and keep the aggregation state of atoms with good thermal stability. Those phases all have good thermal stability, which can greatly promote the high temperature properties of the alloy.
In Section 3.2, it was observed that the peak tensile properties of both BA and MA appeared at the solution temperature of 520 • C. When the solution temperature is higher than 520 • C, the tensile properties of both alloys tend to decline, but UTS and YS of the MA increased by 7.17% and 24.29%, respectively, and the %EL decreased by 26.39%. When the solution temperature raised to 540 • C, the UTS and YS of the modified alloy MA increased by 39.46% and 85.71%, respectively, compared with the BA, and the %EL increased by 69.64% compared with the BA. Based on the SEM/EDS scanning results of Cu and Mg atoms in Section 3.3, the reason for this phenomenon is that the Cu and Mg atomic groups in Al-Si-Cu-Mg alloy have been dissolved and homogenized at 520 • C, and the main strengthening phases, Al 2 Cu phase (3#,4#), and Q-Al 5 Cu 2 Mg 8 Si 6 phase (5#) have been dissolved, so the tensile properties of the alloy will be improved. The melting point of the Al 2 Cu phase is 523 • C, and the melting point of the Q-Al 5 Cu 2 Mg 8 Si 6 phase is 533 • C; therefore, when the alloy is kept at a temperature higher than this temperature for a long time, the traditional microstructure which can improve the tensile properties at room temperature has almost completely dissolved, which can not hinder the migration of dislocation [16], and the tensile properties of BA alloy decrease sharply. The intermetallic phases, such as the rich CrVTi phase, rich TiVMo phase, rich MnMoFe phase, and rich TiVZr phase contained in MA, can exist stably and do not dissolve at high temperatures; these intermetallic phases are pinned at the grain boundary, so the diffusion deformation of the grain boundary can be hindered to a certain extent, thus preventing the generation of microcracks. There is also a large transition in the reduction response of tensile properties of BA and a small transition of MA when the solution temperature is above 520 • C. Similarly, when stretching at a high temperature, the bonding force between the matrix material and the second phase will become weak with the increase in solution temperature. For some traditional intermetallic phases, the adjacent relationship between atoms will be lost at 160 • C, and the grain boundary will undergo diffusion deformation, which will greatly reduce the alloy's mechanical properties; however, even though some traditional second phases in MA with transition metal elements are in an unstable state, due to the existence of high-temperature stable phases, defects such as dislocation can still be hindered, so that the strength index of the alloy can still maintain a high level.
In terms of the fracture mechanism, in plastic deformation, the strength of the intermetallic phase is much greater than that of the matrix, so the intermetallic phase can play a role in preventing the slip. As a result of the slip, stress concentration occurs at the boundary between the intermetallic phase and the slip plane. With the increase in strain, the more dislocations in the plug group, the more stress concentration. When the concentrated stress is equal to the strength of the intermetallic phase, it will lead to the fracture of the intermetallic phase. Compared with the direct fracture of the matrix, the fracture process of the intermetallic phase needs more energy, which increases the difficulty of material fracture; therefore, the existence of the Al 13 (MoCrVTi) 4 Si 4 (18#) phase can increase the fracture limit of the material; however, at the same time, many secondary cracks were observed in the Al 13 (MoCrVTi) 4 Si 4 (18#) phase, which indicates that the Al 13 (MoCrVTi) 4 Si 4 (18#) phase is still brittle. This means that although the Al 13 (MoCrVTi) 4 Si 4 (18#) phase can increase the high-temperature tensile properties of the alloy, it will also reduce the toughness of the alloy.
The Al 74 Si 6 Mn 4 Cr 2 Fe (15#) and Al 85 Si 5 Mn 2 Mo 2 CrFe (16#) phases are also brittle phases. Although the Al 74 Si 6 Mn 4 Cr 2 Fe (15#) and Al 85 Si 5 Mn 2 Mo 2 CrFe (16#) phases also fracture, there is no secondary crack on the phases, which means that the brittleness of the Al 74 Si 6 Mn 4 Cr 2 Fe (15#) and Al 85 Si 5 Mn 2 Mo 2 CrFe (16#) phases is less than the Al 13 (MoCrVTi) 4 Si 4 (18#) phase. It also shows that the toughness of the Al 74 Si 6 Mn 4 Cr 2 Fe (15#) and Al 85 Si 5 Mn 2 Mo 2 CrFe (16#) phases decreases by less than that of the alloy. It is worth noting that the morphology of the (AlSi) 2 (CrVTi)Mo (17#) phase is complete, and the fracture path is along the boundary of (AlSi) 2 (CrVTi)Mo (17#) phase. When the fracture behavior reaches the (AlSi) 2 (CrVTi)Mo (17#) phase, it can prevent the extension of dislocation. Because of its good plasticity, the intermetallic phase does not break, so the crack can only extend along the morphological boundary of the (AlSi) 2 (CrVTi)Mo (17#) phase, which increases the energy needed for fracture, and has a positive effect on its strength but no negative effect on the toughness index of materials. It thus is proven that the (AlSi) 2 (CrVTi)Mo (17#) phase has a positive effect on the strength and plasticity of the material.

Conclusions
The MA was prepared by adding the transition metal elements Cr, Ti, V, Zr, Mo, and Mn into BA. Based on the data obtained by a tensile test after treatment at different solution temperatures and a high-temperature tensile test at different test temperatures, the following conclusions can be drawn: Although transition metal elements are added to MA, the tensile properties of both alloys reach a peak at 520 • C. When the solution temperature is higher than 520 • C, the decrease in tensile properties of MA is much slighter than that of BA.
At all test temperatures (25-300 • C), the strength values of MA with transition metal elements are better than that of BA, and this advantage will be more obvious when the test temperature is higher than 160 • C. Compared with BA, the UTS and YS of the MA increased by only 1.36% and 3.44% at room temperature, 3.41% and 6.85% at 160 • C, 17.49% and 31.65% at 240 • C, and 71.28% and 74.73% at 300 • C, respectively.
The addition of transition metal elements Cr, Ti, V, Zr, Mo, and Mn changed the microstructure of the Al-Si-Cu-Mg alloy. Based on the inherent basic intermetallic phases, there are 13 kinds of intermetallic phases, such as the rich TiVZr phase: (AlSi) 3  Cu and Mg atomic groups were partially dissolved at 500 • C, and can be completely dissolved and homogenized when the temperature reaches 520 • C; Zr, V, and Ti atomic groups can still remain aggregated at 520 • C, and begin to dissolve and homogenize when the temperature is higher than 520 • C; however, Cr, Mo, and Mn atomic groups can remain aggregated at 560 • C without dissolution.
The intermetallic phases containing transition metal elements can exist stably at high temperature, and the thermal stability of the rich MoMnFe, rich TiVMo, and rich CrVTi phases is better than that of the rich TiVZr phase. When the alloy works at a high temperature, the traditional phases lose its strengthening effect, but due to these hightemperature stable phases, it can still hinder the defects such as dislocation, so that the strength index of the alloy can still maintain a high level.
The Al 74 Si 6 Mn 4 Cr 2 Fe, Al 85 Si 5 Mn 2 Mo 2 CrFe, Al 13 (MoCrVTi) 4 Si 4 , and (AlSi) 2 (CrVTi)Mo phases have a positive effect on the tensile strength of the alloy at high temperature; however, compared with the other three phases, the (AlSi) 2 (CrVTi)Mo phase can improve the tensile strength of the alloy and has no negative effect on the plasticity of the alloy.