Open access peer-reviewed chapter

Effect of Microalloying Elements on the Heat Treatment Response and Tensile Properties of Al-Si-Mg Alloys

By Mohamed F. Ibrahim, Mohamed H. Abdelaziz, Herbert W. Doty, Salvador Valtierra and Fawzy H. Samuel

Submitted: March 30th 2017Reviewed: August 22nd 2017Published: December 20th 2017

DOI: 10.5772/intechopen.70665

Downloaded: 456

Abstract

This study was carried out on a series of heat-treatable Al-Si-Mg alloys to determine the effects of Fe, Mg, Sr and Be addition on their microstructural characteristics and tensile properties. The results showed that the eutectic temperature was reduced by 10°C with 0.8 wt% Mg addition. The solidification curves and first derivatives of Sr-free alloys with high Fe and Mg contents revealed a peak at 611°C consequent to the formation of a script-like Be-Fe (Al8Fe2BeSi) phase, which was very close to the peak for α-Al. The morphology of the β-iron platelets underwent changes due to their dissolution, thinning, necking, and fragmentation with increase in solutionizing time. Increased Mg contents are beneficial to the tensile properties unlike the detrimental effect of increasing Fe contents. Additions of Be and Sr noticeably improved the properties at the same Fe and/or Mg contents, the enhancements being markedly observed at higher Mg contents and reduced Fe levels. At high Fe levels, addition of Be is preferable as it neutralizes the deleterious effects of Fe in these alloys; however, addition of 500 ppm Be is inadequate for interacting with other alloying elements.

Keywords

  • aluminum alloys
  • Minitab
  • scattered plot
  • intermetallics
  • Si coarsening

1. Introduction

The main objectives of heat-treating cast Al-Si-Mg alloys include homogenization, stress relief, improved dimensional stability, and optimization of the strength and ductility parameters. The T6 heat-treated Al-Si-Mg alloys have an optimum combination of strength and ductility. The typical heat treatment specification of a T6 temper consists of solid solution treatment and quenching, followed by aging. The main effects of solution heat treatment are the dissolution of Mg2Si particles, the homogenization of the casting, and modification of the morphology of eutectic silicon through fragmentation and spheroidization at critical temperatures. The recommended solution temperature for 356 and 357 alloys is 540 ± 5°C [1, 2].

The purpose of quenching is to preserve the solid solution formed at the solution heat treatment temperature by rapid cooling to room temperature. The quenching medium and rate are the parameters which control the mechanical properties. The highest strength can be ensured when the material is subjected to a rapid quenching rate. Aging is the final stage of heat treatment in cast Al-Si-Mg alloys. The aging can be natural or artificial. Alloy mechanical properties depend on both aging temperature and time. The main objective of artificial aging is to heat the as-quenched castings to an intermediate temperature between 150 and 200°C for 4–8 h in order to precipitate the excess solutes which were supersaturated in α-Al during the solution heat treatment process. The improvement achieved in the mechanical properties during artificial aging is due to the precipitation of metastable phases from the supersaturated solution. Al-Si-Mg alloys fulfill the following precipitation sequence [3]:

SS → needle-shaped GP zones → rod-like β precipitates → platelets of Mg2Si.

For Al-Si-Mg alloys, the solubility of Mg and Si in the Al matrix decreases with temperature. In order to obtain a maximum concentration of Mg and Si particles in solid solution, the solution temperature should be close to the eutectic temperature. For the 356 and 357 alloys, the solution temperature is 540 ± 5°C. At this temperature, about 0.6% Mg can be placed in solid solution. The dissolution of Mg2Si into Mg and Si occurs in the two alloys at 475 and 540°C, respectively [4].

An investigation [5] was carried out on the effects of T6 and T4 tempers on the tensile properties of nonmodified and Sr-modified A356 alloys obtained from permanent mold and sand mold castings. The results showed that the yield strength is not appreciably influenced by the change in Si-particle characteristics. The ultimate tensile strength (UTS) and %El increases significantly with increase in the solution treatment time at 540°C. Also it was observed that upon modification with Sr the fracture mode changes from brittle to ductile especially in sand castings. Both non-modified and Sr-modified alloys obtained from permanent mold casting, however, showed ductile fracture mode. All the improvements in the tensile properties reported upon were related mainly to the changes which occurred in the Si particle aspect ratio and particle size during solution treatment.

Yoshida and Arrowood [6] studied the effects of varying the solutionizing parameters (time and temperature) of a T6 traditional treatment on the mechanical properties (i.e., hardness, ductility, and ultimate tensile strength) of Sr-modified and nonmodified permanent mold cast A356 alloys. The investigated solution treatment times were 2, 4, 8, 16, and 32 h, while the solution treatment temperatures were 520 and 540°C, where the aging treatment was kept unchanged at 160°C for 6.5 h. The highest hardness was obtained at the shortest solutionizing time of 2 h for both the unmodified and modified A356 alloy, while the highest ductility was not reached until the samples were solutionized for 8 h at the same temperature. A slight change in solutionizing temperature did not cause much variation in hardness, ductility, or UTS. It may also be concluded that the Sr-modified samples exhibit higher ductility than the unmodified ones under all the heat treatment conditions reported in this study.

A valuable study was carried out by Moustafa et al. [7, 8] on A413. 1 Al-Si eutectic alloys, where they reported that alloys with Mg contents suffered reduction in hardness, yield strength, and ultimate tensile strength values following the addition of Sr. They explained this observation in terms of retarded precipitation of Mg2Si particles during the aging treatment owing to longer incubation period preceding the commencement of precipitation, irrespective to the solutionizing time [8, 9]. Also, alloying element additions of Mg and Be, resulted in improving the hardness and strength of the base alloy, especially in the T6 condition, where adding small amount of Be (∼0.02%) prevented Mg oxidation (i.e., formation of MgO and MgAl2O4 (spinel)) during melting, so that the hardness increased slightly.

The main purpose of this study, on Al-Si-Mg type 356 and 357 casting alloys, is to investigate the effects of alloying elements and heat treatment conditions on the microstructure and mechanical behavior of nonmodified and Sr-modified 356- and 357-type alloys by examining the following factors:

  1. The influence of alloying elements on the aging behavior of alloy castings investigated in relation to:

    1. Fe content, Sr-modification, grain refining, and addition of Mg and Be; and

    2. Solution heat treatment and aging parameters.

  2. Microstructural analysis of the precipitated phases during the solidification process.

  3. Correlating the results obtained from the tensile testing with the microstructural analysis to determine the effects of each alloying element, intermetallic phase, changes in the morphology, solutionizing parameter, and aging condition on the mechanical properties of the alloys investigated.

2. Experimental procedure

The chemical composition of the B356.2 alloy used in the present study is shown in Table 1. The Mg level of the alloy was increased by adding pure Mg to the alloy melts to obtain Mg levels of 0.4, 0.6, and 0.8 wt%. The Fe and Be were added in the form of Al-25% Fe and Al-5% Be master alloys, respectively, to the alloy melt to obtain Fe levels of 0.09, 0.2, and 0.6 wt% and a Be level of 0.05 wt%. The Sr and Ti were added in the form of Al-10% Sr and Al-5% Ti master alloys, for Sr-modification and grain refining purposes, respectively, to the alloy melts to obtain levels of 0.02 wt% Sr and 0.15 wt% Ti.

AA alloy no.*Chemical composition (wt%)**
SiFeCuMgZnAl
B356.27.0<0.06<0.0250.35<0.001Bal

Table 1.

Chemical composition of the B356.2 alloy (wt%) [8].

AA, aluminum association.


Unlisted aluminum or impurities.


An electrical resistance furnace with a 70-kg crucible capacity was used to prepare 60 kg of each alloy. The melt was kept at 750 ± 5°C as the melting temperature at which additions of magnesium, iron, beryllium, strontium, and titanium were made. These measured additions were added to the melt using a perforated graphite bell. Before casting, the melt was degassed using pure and dry argon for 20 min using a graphite impeller in order to clean the melt from hydrogen and inclusions. For the purposes of thermal analysis, one sample of each alloy composition was prepared using the arrangement shown in Figure 1; moreover, two samplings for chemical analysis were also taken from each melt, one before the start of casting and one at the end of casting.

Figure 1.

Schematic drawing showing the graphite mold used for thermal analysis.

The chemical analysis was carried out using arc spark spectroscopy at GM facilities in Milford, NH. The actual chemical composition of each of the alloys prepared is shown in Table 2, representing average values taken over three spark measurements made for each chemical analysis sample. The alloys A1 through C3B shown in the table represent 18 non-modified alloys while their Sr-modified counterparts were coded A1S to C3BS, respectively. The Sr level ranged from 0 to 0.02 wt% in these alloys. The codes A, B, C, 1, 2, etc. are explained below.

Alloy codeElement concentration (wt%)
SiFeMgCuMnTiSrBeAl
A1*7.020.1010.3760.0500.0100.1430.001Bal.
B17.000.2030.3830.008<0.0010.1510.001Bal.
C16.970.6300.3720.0110.0020.1740.001Bal.
A26.990.1130.5900.0420.0080.1640.001Bal.
B27.030.2100.5700.0090.0020.1790.001Bal.
C26.8806200.5400.0100.0020.1720.001Bal.
A37.080.1230.7600.0340.0070.1920.002Bal.
B37.350.2260.7500.0090.0020.1970.001Bal.
C37.070.6300.7500.0100.0030.1830.002Bal.
A1B*7.330.0930.3680.0520.0060.1800.0010.034Bal.
B1B6.610.1970.4740.011<0.0010.1800.001>0.036Bal.
C1B6.890.6700.5100.0110.0020.1860.003>0.036Bal.
A2B7.260.0810.5300.006<0.0010.1730.001>0.036Bal.
B2B6.600.1840.7100.007<0.0010.1770.001>0.036Bal.
C2B6.220.6800.7000.0070.0020.1830.001>0.036Bal.
A3B6.500.1270.9800.0340.0060.2030.0010.026Bal.
B3B6.380.1960.9600.0090.0010.2100.001>0.036Bal.
C3B5.960.5600.9200.0090.0030.2210.002>0.036Bal.
A1S7.060.1030.3380.0460.0100.1390.016Bal.
B1S7.180.2170.3540.0140.0020.1650.019Bal.
C1S7.180.6600.3490.0070.0020.1720.017Bal.
A2S7.070.1050.5200.0330.0020.1560.018Bal.
B2S7.260.2170.5300.0090.0010.1690.015Bal.
C2S7.170.6400.5300.0080.0020.1540.017Bal.
A3S7.980.1010.8200.0350.0020.1520.013Bal.
B3S7.260.1850.7300.0300.0020.1710.009Bal.
C3S6.840.7100.8600.0340.0050.1690.006Bal.
A1BS6.540.1220.6400.0410.0070.2270.048>0.036Bal.
B1BS6.120.1900.4910.009<0.0010.2170.027>0.036Bal.
C1BS7.780.8100.5300.0840.0120.2100.016>0.036Bal.
A2BS7.640.1230.7800.0100.0020.2430.024>0.036Bal.
B2BS5.930.1940.7300.007<0.0010.2270.023>0.036Bal.
C2BS7.060.6700.7100.0070.0020.2220.022>0.036Bal.
A3BS7.260.1050.9500.0200.0020.1880.023>0.036Bal.
B3BS6.330.1940.9500.0210.0020.1890.017>0.036Bal.
C3BS6.210.6900.8500.0330.0050.2070.014>0.036Bal.

Table 2.

Average chemical composition (wt%) of the alloys studied.

A = 0.1% Fe, B = 0.2% Fe, C = 0.6% Fe, 1 = 0.4%Mg, 2 = 0.6% Mg, 3 = 0.75% Mg, S = Sr,*B = Be.

The various alloys were used to prepare castings from which test bars were obtained for tensile testing purposes. With this aim in mind, the degassed molten metal was carefully poured into an ASTM B-108 permanent mold preheated to 450°C, to obtain castings for tensile testing. Figure 2a shows the actual casting obtained whereas Figure 2b shows the dimensions of the tensile bars.

Figure 2.

(a) ASTM B-108 permanent mold used for casting tensile test bars and (b) dimensions of the tensile test bar (in mm).

Following casting in the ASTM B-108 permanent mold, the tensile bars were divided into 13 different bundles (5 bars/bundle); each bundle was subjected to certain heat treatment conditions as follows: 1 bundle was kept in the as-cast condition; 1 bundle was solution treated at 540°C for 5 h, then quenched in warm water at 65°C, and was kept in the as-solutionized condition; another bundle was kept also in the as-solutionized condition, however, after solutionizing for 12 h at 540°C followed by quenching in warm water at 65°C; 5 bundles were solution heat-treated at 540°C for 5 h, then quenched in warm water at 65°C followed by artificial aging at 160°C for 2, 4, 6, 8, and 12 h, respectively; the remaining 5 sets (bundles) were solution heat-treated at 540°C for 12 h, then quenched in warm water at 65°C followed by artificial aging at 160°C for 2, 4, 6, 8, and 12 h, respectively. The solution and aging heat-treatments were carried out in a forced-air Blue M electric furnace equipped with a programmable temperature controller, accurate to ±2°C. The aging delay was less than 10 s. For each individual heat treatment, five test bars were used.

For each condition, the test bars were pulled to fracture at room temperature at a strain rate of 4 × 10−4/s using an MTS Servohydraulic mechanical testing machine. During the course of the tensile test, an attachable strain-gauge extensometer was connected to the gauge section of the tensile bars to measure the percentage elongation. The reported tensile data were the percentage elongation to fracture (%EF), 0.2% offset yield strength, and ultimate tensile strength; these data were reported as the average values of five data sets obtained from pulling five bars per condition.

Samples for microstructural analysis were taken from both the tensile-tested bars ~10 mm below the fracture surface and the as-cast thermal analysis castings, which were sectioned to study each alloy condition, that is, for the tensile-tested bars, one sample was used in the as-cast condition, while the other two were solution heat-treated (540°C/5 h and 540°C/12 h) beside the as-cast thermal analysis sample. The microstructures of the polished sample surfaces were examined using an optical microscope linked to a Clemex image analysis system, and a Hitachi S-4700 field emission scanning electron microscope (FE-SEM), equipped with a standard secondary electron detector (SE), a backscatter electron detector (BSD), and an energy dispersive X-ray spectrometer (EDS).

3. Results and discussion

3.1. Eutectic Si particles

Measurements of the dendrite arm spacing (DAS) showed that the DAS was about 24 μm in the as-cast tensile bars. The Si particle measurements for the A1 base alloy, containing low levels of Mg and low Fe, and modified base alloy A1S, show that the Si particle area decreased from 28.4 to 0.67 μm2, the Si particle length decreased from 10.8 to 1.25 μm (as can be seen from Figure 3), the aspect ratio decreased from 3.78 to 1.84, while the roundness ratio increased from 18.9 to 50.3% upon addition of Sr to the A1 base alloy in the as-cast condition [9, 10, 11, 12, 13, 14].

Figure 3.

Average length of eutectic silicon particles with different solution heat treatment conditions.

The addition of Be in alloy A1B1 resulted in reduced silicon particle area of 10.3 μm2, a reduced silicon particle length of 6.6 μm, a lower value of aspect ratio (2.73), and an increased roundness ratio up to a value of 35.7%. The mutual addition of Sr and Be (alloy A1BS) led to a reduction in silicon particle area (1.31 μm2), silicon particle length (1.84 μm), and the aspect ratio (1.94); however the roundness ration increased to 47.6%. By increasing the Fe and Mg content (alloy C3), the silicon particle area decreased to 6.9 μm2, the silicon particle length and aspect ratio reduced to 6.44 μm and 3.01, respectively, while the roundness ratio increased to 24.6%. The combined addition of strontium, beryllium, iron, and magnesium (alloy C3BS) reduced the silicon particle area to 1.53 μm2, the silicon particle length to 2 μm, the aspect ratio to 1.99 and increased the value of the roundness ratio to 46.7%. The aforementioned values of the silicon particle characteristics highlight the modification effect of Sr and the partial modification effect of both Mg and Be. However, with increasing Fe levels it seems that most of the Be reacts with the Fe forming a Be-Fe phase (Al8Fe2BeSi). The results for the average Si particle length are summarized in Figure 3.

Figure 4 shows the morphology of the eutectic Si particles in the A1 alloy, deeply etched in hydrofluoric acid (HF) solution. As can be seen in Figure 4a, the Si particles precipitated in the form of short platelets with sharp angles (white arrow). Solutionizing at 540°C resulted in fragmentation of the Si particles as demonstrated by the circled area in Figure 4b. As inferred from Figure 4c, there is a large difference in the particle sizes (see arrow) caused by dissolution of these particles in the aluminum matrix leading to coarsening of the other particles and hence the reported standard deviation (100%). Another observation that could be made from Figure 4c is that the new fragments of the Si platelets are still maintaining the platelet shape as shown by the more elongated particles in the figure. This process continued even after solutionizing for 400 h at 540°C as displayed in Figure 4df.

Figure 4.

Variation in eutectic Si particles in A1 alloy as a function of heat treatment: (a) as cast, (b and c) after 5 h at 540°C, (d) after 12 h at 540°C, (e) after 200 h at 540°C, and (f) after 400 h at 540°C. The white arrow in (f) reveals the dissolution of fine particles even after the long solutionizing time at 540°C.

Figure 5 shows the microstructure of A1S alloy. As expected, addition of Sr 160 ppm resulted in changing the morphology of the Si particles to fibrous as displayed in Figure 5a. The microstructure of the A1S alloy following solutionizing at 540°C for 5 h is presented in Figure 5b. Three observations could be made from this figure:

  1. Necking of the Si particles-solid arrow

  2. Dissolution of some particles in the matrix-broken arrow, in keeping with the: Ostwald ripening mechanism [15] (see Figure 6).

  3. Coarsening of other particles by collision.

Figure 5.

Variation in eutectic Si particles in A1S alloy as a function of heat treatment: (a) as cast, (b) after 5 h at 540°C, (c and d) after 12 h at 540°C, and (e) after 200 h at 540°C, and (f) after 400 h at 540°C broken arrow in (b) points to the presence of very small Si particles, whereas the solid arrow in (e) indicates the complete fusion of a Si particle in a cluster of particles.

Figure 6.

Schematic diagram showing coarsening of Si particles according to Ostwald ripening mechanism [15].

Increasing the solutionizing time to 12 h at 540°C led to partial spheroidization as shown by the solid arrows in Figure 5c where the new particles are having multiple sides. The white area circled in Figure 5c points to particle collision. Figure 5d is an enlarged portion of Figure 5c showing the possibility of the fusion of some particles in the background to the left, leading to a coarser one. This process of coarsening was observed to continue up to 400 h at 540°C, Figure 5df. It should be noted here that the Si particles are not spherical; rather, they possess multiple faces (Figure 5f).

3.2. Precipitation of Mg2Si

Samuel et al. [16] observed that any Sr-modified microstructure is clearly affected when magnesium is present. Microstructural parameters as obtained from image analysis, such as silicon particle size and aspect ratio, were found to increase with an increasing Mg content, subsequently becoming increasingly inhomogeneous. The reason for the deterioration in modification is believed to be the formation of intermetallic phases of the type Mg2SrAl4Si3, where the addition of Mg also lowers the eutectic temperature - the eutectic temperature decreases with increasing Mg content. It was also reported, however, that a magnesium content of ~1 wt% itself acts as a refiner for the eutectic silicon in unmodified Al-Si alloys.

Ibrahim et al. [17] showed that the addition of up to 0.5 wt% of Mg to molten 319 type alloys results in the formation of Mg2Si; the Mg-rich phase commonly exists as rounded black particles close to the eutectic silicon particles. It was also reported that the addition of Mg results in remarkable fragmentation/modification of the eutectic silicon particles as well as transformation of a large portion of the harmful needles of β-Al5FeSi Fe phase into the less detrimental Chinese script-like phase with a composition close to Al8Mg3FeSi6.

The heat treatment for Al-Si-Mg alloy is T6 which consists of solution heat treatment and natural or artificial aging. A solution treatment between 400 and 560°C, results in the dissolution of the hardening phase (Mg2Si) in the aluminum matrix. However, the solutionizing temperature is limited by the eutectic phase melting temperature. The alloy thereafter is aged at low temperature (150–200°C) for precipitation of the hardening compounds which improves the mechanical properties of the aluminum matrix [18]. The primary purpose of the long solution treatment is to thermally alter silicon particle characteristics [19]. During T6 treatment, the Mg and Si which are in solid solution precipitate as Mg2Si during the aging treatment [13].

Figure 7a reveals the precipitation of Mg2Si in the form of Chinese script (black) following the formation of π-Al8Mg3FeSi6 in 356 alloy solidified at 0.8°C/s (A1 alloy). The identity of these two phases was confirmed from their corresponding EDS spectra shown in Figure 7b and c, respectively. The microstructure of the A1 alloy following solutionizing at 540°C for 12 h is shown in Figure 8a, revealing the presence of scattered particles. These particles have been identified as Si particles [20]. Following aging at 160°C for 12 h resulted in the dense precipitation of Mg2Si particles in the form of short rods-Figure 8b. Obviously, the density of the Mg2Si precipitation is controlled by the amount of added Mg and the presence of Sr [21]. Another parameter to be considered during long solutionizing times is the decomposition of the π-phase into the β-phase as demonstrated in Figure 9 [22].

Figure 7.

Precipitation of Mg2Si and π-Fe in 356 alloy solidified at 0.8°C/s: (a) backscattered electron image, (b) EDS spectrum corresponding to Mg2Si phase, and (c) EDS spectrum corresponding to π-phase.

Figure 8.

Backscattered electron images of the precipitation observed in A1 alloy tensile bars: (a) T4 condition and (b) T6 condition.

Figure 9.

Decomposition of π-phase to β-phase during solutionizing at 540°C for 12 h [22].

3.2.1. Tensile properties

Tensile properties of reference alloys A1, A3, and C3 in the as-cast and different heat treatment conditions applied are summarized in Table 3. In the as-cast samples, increasing Mg content from 0.4 wt% (base alloy A1) to 0.8 wt% (alloy A3) resulted in slightly increasing the strength due to the partial modification effect of Mg as well as the transformation of β-phase to π-phase, that is, most of the Fe-intermetallic phases precipitated in the form of the π-phase in spite of the low Fe content (0.09 wt%), whereas increasing the Fe level up to 0.6 wt% in the high Mg-containing alloy A3 i.e. alloy C3 resulted in decreasing the UTS somewhat, because of the growing formation of Fe-intermetallic phases. For the three reference alloys, percent elongation was decreased.

Alloy codePropertyAs-castSHT
5 h
Aging time (h)—SHT 5 h
246812
A1UTS (MPa)204262342358361354360
YS (MPa)97116237267277282292
El (%)6.515.9108.78.16.26.5
A3UTS (MPa)204263343358381383386
YS (MPa)114141254292330333347
El (%)3.47.25.964.33.12.82.0
C3UTS (MPa)201239320328366366360
YS (MPa)116135270297345350357
El (%)2.64.81.71.01.00.90.7
Alloy codePropertyAs-castSHT
12 h
Aging time (h)—SHT 12 h
246812
A1UTS (MPa)204255340358360362362
YS (MPa)97107229273284274280
El (%)6.517.612.3108.79.58.5
A3UTS (MPa)204287351368382382384
YS (MPa)114154266295321336353
El (%)3.49.76.53.64.02.72.0
C3UTS (MPa)201250317334367365364
YS (MPa)116152294301317326327
El (%)2.64.31.01.00.90.70.7

Table 3.

Tensile properties of reference alloys A1, A3, and C3 in the as-cast and heat-treated conditions.

Applying 5 h solution heat treatment at 540°C appeared in a noticeable increase in the ultimate strength (UTS) values, (59 MPa) for alloys A1 and A3, and (39 MPa) for alloy C3, due to the fragmentation and spheroidization of Si particles and spheroidization of undissolved π-phases as well as dissolving of Mg2Si in the matrix and the decomposition of the π-phase to β-phase which further fragmented during solution heat treatment, thereby improving the tensile properties. For both solutionizing times, the elongation values obtained were two times or more higher than those observed in the as-cast condition for alloys A1, A3, and C3, indicating improved ductility of the solution heat-treated samples. Similar results regarding the addition of alloying elements and solution heat treatment parameters have been reported in a number of studies [23, 24, 25, 26, 27, 28, 29, 30].

The tensile data of the 31 alloys used in the present work was classified into 4 series:

  1. Fe-Mg series.

  2. Fe-Mg-Be series.

  3. Fe-Mg-Be-Sr series.

  4. Fe-Mg-Sr series.

The data was then treated using Minitab software and is presented in Figures 1012.

Figure 10.

Variation in the UTS values as a function of alloying elements.

Figure 11.

Variation in the YS values as a function of alloying elements.

Figure 12.

Variation in the % elongation to fracture (EF) values as a function of alloying elements.

Based upon the results presented in these figures, the following observations may be noted:

  1. In the as-cast condition, increasing the Mg content leads to further transformation of the β-phase platelets to a Chinese script π-phase, regardless of the Fe content, thereby decreasing the harmful effect of the β-phase.

  2. Increasing the solution heat treatment time leads to further decomposition of the π-phase, fragmentation of the β-phase, and spheroidization of the eutectic Si, resulting in an improvement in the alloy tensile properties.

  3. Increasing the Fe level decreases the alloy ductility values, whereas the addition of Mg increases the % EF-values.

  4. Introducing Be, Sr, or both, improves the alloy strength to some extent, regardless of the levels of Fe and Mg present.

  5. Increasing solution treatment time from 5 to 12 h enhances the UTS and YS values.

  6. Increasing the Mg-content results in improving the tensile properties; however increasing the iron levels markedly deteriorates these properties.

  7. Additions of Be and Sr noticeably improves the mechanical properties of the alloys with the same Fe and/or Mg contents; however, these enhancements in mechanical properties are markedly observed at higher Mg contents and reduced levels of Fe.

It is evident from Figure 13a that Fe is the major element in determining the alloy performance. Introduction of Sr or Be or both would help in minimizing the harmful effect of Fe but to a limited extent. Increasing the solutionizing time to 12 h improved the alloy ductility due to coarsening of the eutectic Si particles. Figure 13b shows the UTS values of all the 36 alloys used in the present study for a solutionizing time of 5 h. It is clear that most of the T6 values are falling within a narrow zone represented by the oval circle moving the major axis to somewhat higher UTS levels with an increase in the UTS range (arrows). With increase in the solutionizing time from 5 to 12 h (Figure 13c), the width of the oval circle increased, accompanied by a slight drop in the major axis direction to lower UTS levels.

Figure 13.

The 3D scattered plot of UTS versus %EF versus aging time: (a) base alloy, (b) all alloys in the T6 condition following solutionizing for 5 h at 540°C, and (c) all alloys in the T6 condition following solutionizing for 12 h at 540°C. The black arrows indicate the major axis of the oval circles.

4. Concluding remarks

The present work was carried out on a series of heat-treatable aluminum-based aeronautical alloys containing various amounts of magnesium (Mg), iron (Fe), strontium (Sr), and beryllium (Be). From an analysis of the results obtained, the following concluding remarks may be made.

  1. The addition of beryllium produces partial modification of the eutectic silicon particles in a manner similar to that reported for the addition of magnesium. The eutectic temperature was reduced by 10°C as a result of the addition of 0.8 wt% Mg. The solidification curves and their derivatives of Sr-free alloys with high Fe and Mg contents showed that there was a peak at 611°C consequent to the formation of a Be-Fe (Al8Fe2BeSi) phase, this peak was very close to the peak corresponding to the formation of α-Al. The morphology of the Be-Fe phase was recognized to be a script-like one.

  2. Increasing the duration of solution heat treatment enhances the tensile properties of the alloys through the decomposition of the π-iron phase into the β-iron phase, fragmentation of the β-phase, and change in the geometry of both π-phase and silicon particles (i.e., spheroidization). Two mechanisms of eutectic Si particle coarsening during solution heat treatment were observed to occur: (1) Ostwald ripening in the solution and (2) clustering/collisions of the Si particles. Coarsening increases with increased solution heat treatment time.

  3. Higher Mg contents are believed to be beneficial to the tensile properties (i.e., ductility, ultimate tensile strength, and yield strength) in that they oppose the detrimental effect of increasing the Fe content on the same tensile properties. Additions of Be and Sr noticeably improve the mechanical properties of the alloys with the same Fe and/or Mg contents; however, these enhancements in mechanical properties are markedly observed at higher Mg contents and reduced levels of Fe. In the case of high levels of Fe, addition of Be is preferable because it neutralizes the deleterious effects of Fe phases in cast aluminum-silicon alloys; though adding 500 ppm of Be, in case of high Fe contents, is inadequate to interact with other alloying elements. During the melting process, the possible existence of a Be-Sr phase (probably SrBe3O4) is believed to consume some of the Be content in the alloy, leading to both reduction in the free Be content as well as the alloy mechanical properties.

  4. The alloy tensile properties are highly affected by varying the solutionizing and aging treatments times. In the 356 base alloy, the main strengthening effects were confirmed to be related to the formation of Mg2Si precipitates. The improvements in the yield strength values are attributed to higher Mg contents, lower levels of Fe, addition of Be, Sr-modification, and solutionizing and aging times. Such enhancements in yield strength values are of great importance to the aeronautical industry because the design considerations in that field are mainly influenced by the yield strength.

Acknowledgments

The authors would like to thank Amal Samuel for enhancing the quality of the images and figures used in the present manuscript. They also wish to thank Dr. A.M. Samuel for careful proofreading of the manuscript.

© 2017 The Author(s). Licensee IntechOpen. This chapter is distributed under the terms of the Creative Commons Attribution 3.0 License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

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Mohamed F. Ibrahim, Mohamed H. Abdelaziz, Herbert W. Doty, Salvador Valtierra and Fawzy H. Samuel (December 20th 2017). Effect of Microalloying Elements on the Heat Treatment Response and Tensile Properties of Al-Si-Mg Alloys, Solidification, Alicia Esther Ares, IntechOpen, DOI: 10.5772/intechopen.70665. Available from:

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