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# Influence of ordered L12 precipitation on strain-rate dependent mechanical behavior in a eutectic high entropy alloy

## Abstract

Recent studies indicate that eutectic high-entropy alloys can simultaneously possess high strength and high ductility, which have potential industrial applications. The present study focuses on Al0.7CoCrFeNi, a lamellar dual-phase (fcc + B2) precipitation-strengthenable eutectic high entropy alloy. This alloy exhibits an fcc + B2 (B2 with bcc nano-precipitates) microstructure resulting in a combination of the soft and ductile fcc phase together with hard B2 phase. Low temperature annealing leads to the precipitation of ordered L12 intermetallic precipitates within the fcc resulting in enhanced strength. The strengthening contribution due to fine scale L12 is modeled using Orowan dislocation bowing and by-pass mechanism. The alloy was tested under quasi-static (strain-rate = 10−3 s−1) tensile loading and dynamic (strain-rate = 103 s−1) compressive loading. Due to the fine lamellar microstructure with a large number of fcc-bcc interfaces, the alloy show relatively high flow-stresses, ~1400 MPa under quasi-static loading and in excess of 1800 MPa under dynamic loading. Interestingly, the coherent nano-scale L12 precipitate caused a significant rise in the yield strength, without affecting the strain rate sensitivity (SRS) significantly. These lamellar structures had higher work hardening due to their capability for easily storing higher dislocation densities. The back-stresses from the coherent L12 precipitate were insufficient to cause improvement in twin nucleation, owing to elevated twinning stress under quasi-static testing. However, under dynamic testing high density of twins were observed.

## Introduction

While high entropy alloys (HEAs), or multi-principal-component alloys1,2,3,4,5 have attracted the attention of the worldwide scientific community in recent years, most of the focus has been on discovering and investigating single phase solid solution alloys, presumably stabilized by their configuration entropy of mixing, especially at high temperatures. Typically, HEAs based on the face-centered cubic (fcc) crystal structure, such as the widely investigated Al0.1CoCrFeNi and CoCrFeMnNi alloys1,2,3,4,5, have been reported to exhibit excellent room temperature tensile ductility but rather poor strengths, whereas the body-centered cubic (bcc) based HEAs, like those containing refractory elements based on Nb-Mo-Ta-W-V-Mo etc6,7,8, exhibit very high compressive strength values but very limited ductility under tensile loading. Additionally, two-phase bcc +B2 HEAs, such as FeNiMnAl9, exhibiting a fine scale spinodal-like microstructure, exhibit phenomenal compressive yield strengths (~2350 MPa), but no tensile ductility.

A commonly adopted strategy to overcome this strength-ductility tradeoff is to develop multi-phase microstructures, involving at least one ductile/soft and one hard/strong phase, mixed in the appropriate proportion. Common examples include duplex alloys, such as 2205 stainless steel, which have a hard bcc phase to increase the strength of the alloy and a soft fcc phase to maintain the tensile ductility while deformation. The goal has been on fine-tuning the alloy composition and/or processing conditions in order to obtain a material with a good balance between ductility and strength. Eutectic alloys, often exhibiting a two-phase lamellar microstructure, offer such a possibility, and have been investigated for many years in different classes of alloys. Eutectic morphologies are characterized by the simultaneous growth of two (or more) phases from the liquid. A recently developed new class of eutectic HEAs (EHEAs), have attracted a lot of attention due to their promising mechanical properties10,11,12,13,14,15,16,17,18. These eutectic HEAs typically exhibit a lamellar fcc + B2 microstructure, with the ability to tune the composition of both phases over a wide range due to their inherent complexity. The most extensively investigated EHEAs include Fe30Ni20Mn35Al1510,11,12 and AlCoCrFeNi2.111,12,13,14,15,16,17,18. Other EHEA compositions reported are CoCrFeNiMnPdx19 and CoCrFeNiZrx20. Most reports in the published literature on such alloys are based on the as-cast microstructure without any subsequent thermomechanical treatments.

The present study focuses on the marginally hypo-eutectic HEA with the nominal composition of Al0.7CoCrFeNi (15 at. % Al and 21.25 at.% each of Co, Cr, Fe, Ni). While a few previous investigations on this HEA have reported a lamellar two-phase fcc/B2microstructure in this alloy21, a detailed investigation of the microstructure of this alloy and its evolution during post-solidification thermo-mechanical processing forms the basis of the present study. Furthermore, the present study also investigates the influence of such heat-treatments on the mechanical behavior of this alloy under both quasi-static low strain rate tensile loading conditions, as well as dynamic strain rate compression conditions. The results clearly indicate that with suitable heat treatments the fcc phase in the lamellar two-phase microstructure is further strengthened by forming ordered L12 nano precipitates, without compromising the tensile ductility. The fcc + L12/bcc + B2 microstructure in this alloy exhibited a tensile yield strength close to 1000 MPa (~990 MPa), ultimate tensile strength (UTS) ~1400 MPa and elongation to failure of ~13% under quasi-static loading (strain rate of 10−3) whereas flow stresses reaching to over 1800 MPa without failure under dynamic loading (strain rate of 2 × 103). Microstructural assessment after deformation revealed substantial deformation twinning in this alloy at higher strain rates.

## Experimental Methods

### Materials processing

The alloy of composition Al0.7CoCrFeNi (15 at. % Al and 21.25 at.% each of Co, Cr, Fe, Ni) was produced by melting elemental Al, Co, Cr, Fe and Ni mixed in appropriate proportions. Figure 1(b) charts the processing route followed to obtain different microstructures and resulting properties. The as cast alloy was homogenized at 1150 °C for 1 h to annihilate the dislocations and reduce micro-segregations from casting process to assist in cold deformation of the alloy. The SEM microstructure from this condition is shown in Fig. 1(a). The backscattered electron diffraction (BSED) image in Fig. 1(a) shows a two phase eutectic type of microstructure with a bright contrast phase and dark contrast phase organized in lamellar arrangement. The grain boundaries are highlighted by the yellow lines and lamellae directions are shown using red arrows in the figure. The alloy was then rolled at room temperature to 30% reduction in thickness. A subsequent annealing at 1100 oC for 5 mins was done to homogenize and recrystallize the alloy at high temperature. The cold-rolled and homogenized condition is referred as CR-H hereafter. Another low temperature annealing treatment was done at 580 oC for 24 h on the CR-H condition, this is referred as the CR-H-580 condition.

### Microstructural characterization

To analyze the microstructure of the material after processing, pieces were cut and metallographically polished in stages. Final mirror surface finish was achieved by 0.02 µm colloidal silica gel VibroMetTM polishing. The crystal orientations and elemental composition were characterized by electron backscattered diffraction (EBSD) and energy dispersive spectroscopy (EDX), respectively, in a FEI Nova Nano scanning electron microscope (SEM). Lift-out samples for transmission electron microscopy (TEM) and atom probe tomography (APT) were prepared using an FEI Nova 200 dual beam focused ion beam (FIB). TEM analysis was conducted using an FEI Tecnai F20 operated at 200 kV fitted with a STEM-EDS detector. To measure the composition, energy dispersive spectroscopy (Super-X system) equipped on an FEI-TITAN G2 TEM microscope was used in the HAADF STEM mode operating at 300 kV and the results were analyzed with FEI’s ES vision software version 6. The APT experiment was performed with a local electrode atomprobe (LEAP 3000X) with a target evaporation rate of 0.5% per pulse at 45 K. APT data reconstruction and quantitative analysis were performed using a CAMECA visualization and analysis software (IVAS) 3.6.8.

### Mechanical characterization

Dog-bone-shaped tensile specimens with gauge length 3 mm were machined from the rolled and annealed sheets by Electrical Discharge Machining (EDM). Both sides of the specimen were ground using SiC paper to achieve final thickness of ~0.7 mm and gauge width of ~1.0 mm. Tensile tests were performed at an engineering strain rate of 10−3 s−1. Each test was performed at least three times to ensure consistency; representative results are reported herein. These quasi-static tests used a LVDT (linear variable displacement transformer) extensometer to perform at least four independent tests to obtain tensile elongation and strength data. Yield strength, ultimate tensile strength, and elongation to failure were determined from the uniaxial tensile stress–strain curves. Cubes of 3 mm were compressed dynamically using split Hopkinson pressure bar (SHPB) testing machine at 2 × 103 s−1 strain rate.

## Results and Discussion

### Influence of thermo-mechanical processing on microstructure

The SEM microstructure from the CR-H condition of the Al0.7CoCrFeNi HEA is shown in Fig. 1. The SEM backscatter images in Fig. 1(a,c) reveal the lamellar morphology of the two-phase eutectic in this alloy. Depending on the orientation of these lamellar eutectic colonies, with respect to a two-dimensional plane of sectioning, the lamellar structure could appear more globular-like, as seen in some regions of Fig. 1(a). The partitioning of elements into these phases, was determined using SEM-EDS. The dark contrast phase highlighted in blue color in Fig. 1(d), is rich in Al and Ni whereas Cr, Fe and Co partitions to the bright contrast phase(red). The SEM-EDS elemental maps of all the elements are shown in Fig. 1(e–i).

EBSD and TEM experiments were conducted to understand the crystallography of each phase. Figure 2(a–c) show the EBSD results and Fig. 2(d) shows a montage of bright field TEM images from the CR-H condition. The inverse pole figure (IPF) (inset in Fig. 2(a)) and the phase map (Fig. 2(b)) were obtained by consistently indexing the two phases as fcc and bcc. Figure 2(b) shows the area fraction of the two phases with fcc (bright contrast phase in BSED images) being 70% and bcc (dark contrast phase) being 30%. TEM examination from each of these regions revealed that while the fcc phase is disordered the bcc phase exhibits chemical ordering. The bright-field TEM image in Fig. 2(d) clearly shows the fcc phase to be the higher phase fraction phase. Convergent beam microdiffraction patterns from fcc and bcc phases are shown as insets in Fig. 2(d). The presence of extra super lattice spots at {001} positions in the [001]bcc zone axis clearly indicates ordering within the bcc phase. An fcc/B2 microstructure have also been reported earlier in Fe30Ni20Mn35Al15 and AlCoCrFeNi2.1 EHEAs10,11,12,13,14,15,16,17,18, though the morphology of the eutectic microstructure varied with processing route and composition. Liao et al. showed that higher solidification rates not only influence the lamellar width but also the orientation relationship (OR) between the two phases11,12. There is a Kurdjumov–Sach (KS) OR between the fcc/bcc phases(highlighted in blue) wherein {111}fcc{110}bcc and 〈110〉fcc||〈111〉bcc. The pole figures shown in Fig. 2(c) also confirms the presence of KS OR between fcc and bcc phases. In general, multiple ORs including Kurdjumov–Sach (KS), Nishiyama–Wasserman (NW) and Pitsch are possible in fcc/B2 containing AlxCoCrFeNi alloys22.

The entropy of fusion of the two phases, comprising the eutectic, play a very important role in determining the morphology of the resulting microstructure. If both phases possess a low entropy of fusion, their growth is easy along all crystallographic directions and resultant microstructure is a regular lamellar eutectic. Where the low volume fraction phase in the eutectic possesses a high entropy of melting, as do intermetallic compounds, the eutectic microstructure is usually irregular23.

In the Al0.7CoCrFeNi alloy the B2 phase fraction is ~30% and shares an OR with the fcc phase. Consequently, this eutectic exhibits a lamellar-like morphology at a coarser scale, while at the microscopic scale the B2 lamellae are not continuous but are pinched off or broken in many regions, as revealed in Fig. 2(d). This can be probably because B2 is an intermetallic phase with high entropy of melting.

Figure 3(a) shows a HAADF-STEM image from the CR-H condition where the brighter phase is fcc and the darker phase is B2. One-dimensional compositional profiles for the various elements, across the fcc/B2 interface are shown in Fig. 3(b). These results are consistent with SEM-EDS results shown in Fig. 1. The compositions of the two phases are given in Supplementary Table T1. Higher magnification STEM-EDS maps from each phase are shown in Fig. 3(c–f). Note that compositional fluctuations are clearly visible within the B2 regions, as shown in the Cr map in Fig. 3(d) whereas the fcc region does not exhibit such fluctuations (refer to Fig. 3(f)). These fluctuations suggest the presence of a two-phase mixture of possibly B2 (ordered) containing Cr rich nano-precipitates of a disordered bcc phase. This is consistent with the observed diffraction pattern shown in Fig. 2(c) since the overlap of B2 + bcc diffraction patterns along the same zone axis cannot be distinguished from that of a single B2 phase along the same zone axis. Based on the STEM-EDS results and the diffraction pattern, it can be concluded that the B2 lamellae in this EHEA are actually two-phase mixtures of B2 + bcc. Such a decomposition of the B2 phase into B2 + bcc has been previously reported in Al-Co-Cr-Fe-Ni HEAs by Gwalani et al.3.

In the CR-H-580 sample, the microstructure is similar to CR-H condition and is shown in Supplementary Fig. S1. Figure S1(a) shows the BSED image with lamellae of fcc and B2/bcc phases. This is clearly revealed by the EBSD results shown in Fig. S1(b,c). A STEM image from this condition is shown in Fig. 4(a) and the SAD patterns from the two phases are shown as insets. The bcc/B2 region is similar to the CR-H condition where Cr rich bcc nanoprecipitates are present within the B2 phase (Fig. 4(b,c)). The superlattice spots at {001} positions can be noted in the [011]fcc zone which are not seen in CR-H condition. This clearly shows the ordering of the fcc phase as well in CR-H-580 condition. A compositional partitioning within fcc as shown in Fig. 4(d,e) further confirms the presence of fcc + L12 (ordered fcc) phase in this condition.

Atom probe tomography results from the CR-H-580 condition are shown in Supplementary Fig. S2 and Fig. 5. Supplementary Fig. S2 shows a reconstruction from an fcc + L12 region of the microstructure. Fine-scale spherical precipitates with a radius of ~3–5 nm are uniformly distributed within the fcc lamellae. The compositional partitioning across the matrix-precipitate interface is shown by a proximity histogram in the figure. The L12 precipitates are rich in Ni (~55 at. %) and Al (~35 at. %) whereas the matrix consists mainly of Cr (~29 at. %), Fe (~26 at. %) and Co (~25 at.%) with smaller amounts of Ni (~13 at.%) and Al (~7 at.%). The volume fraction of the precipitates is ~9.5% of the total volume of the reconstruction. The compositional details of the B2 and bcc are revealed in another reconstruction shown in Fig. 5. Figure 5(a) shows the fcc/L12 region near the tip of the reconstruction with a sliver of B2/bcc region has been captured in the lower portion. The bcc is identified by the enrichment of Cr (Fig. 5(b)) and B2 contains high concentration of Ni and Al (Al enrichment can be seen in Fig. 5(c)). Note that the Ni concentration is lower in the B2 as compared to the L12 (~55 at. % in L12 and ~30 at. % in B2). The iso-concentration surfaces of Al (green) and Cr (red) are used to delineate the B2/bcc phases in Fig. 5(d) and a cylinder is used to map the 1-dimensional compositional profile (shown in Fig. 5(e) across the two phases. The exact compositions of each phase measured from the APT analysis (also provided in Supplementary Table T2) are as follows (all in at. %):

Fcc: Al-6.7, Co-24.1, Cr-28.8 Ni-14.1 and Fe-26.3 (Al0.25CoCrFeNi0.5)

L12: Al-35.8, Co-4.3, Cr-0.9, Ni-56.4, and Fe-2.6 (Ni2.26, Co0.2, Fe0.1, Cr0.04, Al0.4) Al

B2: Al-33.7, Co-21.7, Cr-0.1, Ni-32.8, and Fe-11.7 (AlCo0.7NiFe0.4)

Bcc: Al-1.9, Co-2.7, Cr-90, Ni-0.5, and Fe-4.9

Note that the ordered L12 phase in this alloy contains an unusually high amount of Al. The substantially higher 35.8 at. % Al in this L12 phase, as compared to the stoichiometric 25 at % based on Ni3Al, suggests that Al anti-site defects are created on the Ni sites of the L12 phase in this alloy. However, detailed first-principles, electronic structure based computational studies need to be coupled with these experimental observations in order to establish the site-occupancies of different elements within the ordered L12 structure. Interestingly, a similar L12 composition was reported in case of the Al0.3CoCrFeNi HEA as well3.

In case of the B2 composition (which is based on a NiAl structure), if we assume that Fe occupies the Ni sites then the approximate formula for the B2 phase (with anti-site defects) could be –(NiFe)(AlCoCr).

#### Effect of microstructure on mechanical properties

The advantage of such a two-phase eutectic alloy is that it consists of a more easily deformable ductile (fcc or fcc + L12) phase, and a hard, difficult to deform, B2 + bcc phase. The hard B2 + bcc phase defines the inter-lamellar spacing of the softer fcc phase. To evaluate the mechanical performance of the Al0.7CoCrFeNi alloy, the CR-H and CR-H-580 conditions were tested under two different strain rates (10−3 s−1 and 2 × 103 s−1) and the corresponding stress-strain plots are shown in Fig. 6. Figure 6(a) shows the engineering (thick line) and true (thin line) stress-strain plots from quasi-static testing. The CR-H condition with fcc + B2 (with fine scale bcc precipitates) shows a yield strength (YS) of ~770 MPa, UTS ~1090 MPa with an elongation to failure (EF) of ~17% under the quasi-static deformation (10−3). The CR-H-580 condition with the fcc + L12 & B2 + bcc microstructure exhibited a YS ~1080 MPa, UTS ~1370 MPa and EF of ~15%. A precipitation strengthening of ~310 MPa is observed after the additional heat treatment with just ~2% reduction in the elongation.

The strength enhancement due to nano-precipitates can be estimated by using a simple Orowan strengthening model based on the dislocation bowing and by-pass mechanism. It can be described by the equation below:

$${\rm{\sigma }}\text{Orowan}=\frac{{\bf{G}}\ast {\bf{b}}}{{\boldsymbol{\lambda }}}$$
(1)
$${\rm{\lambda }}=\frac{{\bf{4}}({\bf{1}}-{\bf{f}}){\bf{r}}}{3{\bf{f}}}$$
(2)

Where λ is average planar center-to-center distance between nano-precipitates, G is the shear modulus of the matrix, b is the Burgers vector (assumed to be 80 GPa and 0.255 nm for CoCrFeNiMn respectively4, r is the radius of the nano-precipitates (3 nm), and f is the volume fraction of precipitates, which is 9.5% by vol. in fcc phase (from APT reconstruction) and is equal to $$9.5\ast 0.7=6.65 \%$$ by vol. in the entire microstructure. Based on Eqs (1) and (2), the Orowan strengthening can be estimated to be ~360 MPa, which compares reasonably well with the experimentally observed strengthening value of 310 MPa.

This alloy strain-hardens substantially under both heat treatment conditions (refer true stress-strain plots in Fig. 6(b)). The work-hardening rate (δσ/δε) versus true strain is shown in Fig. 6(b). Both the heat treatment conditions depict different stages of strain hardening commonly observed in a low SFE material24,25,26 (labeled in Fig. 6(b)). In Stage A, strain hardening shows the steady decrease in the hardening rate which signifies the dislocation mediated plasticity, stage B has a near constant hardening rate and in stage C the hardening rate again decreases steadily. The initiation of stage B has been correlated with the initiation of deformation twinning. Similarly, stage C is correlated with extensive twin intersections in the microstructure24. The decrease of strain hardening in stage C is due to the decreasing rate of primary twinning. In the current study, the steady-state work-hardening rate is marked as stage B in the work-hardening rate versus true strain, in the Fig. 6(b). The steady state work hardening for CR-H condition is ~3000 MPa whereas for CR-H-580 is >4000 MPa. Hence, the precipitation of ordered L12 nano-precipitates strengthened the alloy and improved the strain hardening rate. The details of the associated deformation mechanisms will be discussed further in later section.

A SHPB apparatus was used to conduct the high strain rate (dynamic) deformation test at a strain-rate of 2 × 103 s−1. None of the specimen fail till 20% straining at 2 × 103 s−1 strain-rate. We note that the flow stresses are evidently greater at the high strain rate testing. Hence a strong strain-rate sensitivity (SRS), which is a measure of strengthening of a material at higher strain rates, is observed. For the force equilibrium within the specimen, the elastic waves generated in the SHPB technique needs at least an eight time reverberation27. The stress estimation measured from elastic wave pulses are reliable only after this time. Therefore, as a common practice the stress values prior to 1% strain in the curve are disregarded. The flow-stress in the CR-H condition (at ~1% true strain) is ~1080 MPa and that for CR-H-580 is ~1440 MPa.

The parameter for strain rate sensitivity (SRS), m, is calculated based on the flow stresses at two different strain-rates as following:

$$m={[\frac{\partial \mathrm{ln}\sigma }{\partial \mathrm{ln}\dot{\varepsilon }}]}_{T,\varepsilon }$$
(3)

σ is the flow stress, $${{\rm{\varepsilon }}}^{\cdot }$$ is the strain-rate, T is temperature, and ε denotes strain. The strain rate sensitivity parameter, m at 1% flow stress for the two alloy conditions can be calculated to be 0.017 for CR-H-580 and 0.018 for CR-H condition. A recent study by Li et al.28 on single phase fcc Al0.3CoCrFeNi HEA showed a very high SRS of 0.053. The lamellar dual phase microstructure has a high density of interphases, which increase strength significantly compared to a single phase large grained high entropy alloy28, however they also lessen SRS considerably. The strain rate sensitivity is not affected as much by precipitation of coherent L12 precipitates.

Gangireddy et al.29 examined the microstructural dependency of SRS and concluded that relative contributions from short-range (thermal) and long-range (athermal) obstacles to dislocation motion, determine strain rate sensitivity of yield strength. As slip is the preceding mechanism for deformation, before other mechanisms such as twinning or transformation-induced plasticity can initiate, at small plastic strains, before the differences in deformation mechanisms can affect strength, the yield strength is determined by obstacles to slip alone. The amplitude of long-range obstacles is too large for thermal activation and therefore can be treated as athermal in nature and have no/little dependence on strain rate/temperature. While the short-range obstacles, where thermal activation can help to overcome such barriers, brings the strain rate dependency. Even though fine-scale L12 precipitates increased strength by 30% in aged CR- H-580, they are coherent in nature and thermally activated. So, SRS drops only slightly in this microstructure.

Within the fcc + L12 microstructure of the fcc-based lamellae shown in the APT reconstruction in Fig. 5, there appears a precipitate free channel near the interface of the B2 + bcc and fcc + L12 lamellae (refer Fig. 5). Such precipitate-free channels near the lamellar boundaries were also observed in the high-resolution STEM-EDS maps. These precipitate-free channels can be relatively softer as compared to the fcc + L12 regions, and consequently act as sites for high dislocation storage in the vicinity of the interfaces during deformation. Such a mechanism could potentially rationalize the similar strain rate sensitivity observed in case of the Al0.7CoCrFeNi eutectic HEA, in the absence or in the presence of L12 precipitates within the fcc-based lamellae.

#### Post Deformation characterization

Figure 7 shows the EBSD and TEM results from the CR-H condition after quasi-static deformation. Figure 7(a,b) show the IPF and phase map, where a clear difference in the fcc and bcc regions can be observed, when compared to before deformation structure. The bcc phase is broken into smaller grains and segmented. It is difficult of notice any deformation twin at this magnification. More details are obtained upon TEM examination. A TEM foil was FIB prepared from a region near to the failure under quasi-static tensile testing. A BFTEM image showing the fcc and bcc regions is displayed in Fig. 7(c). The SADPs from [001] fcc and [111]fcc are shown in the bottom of the image whereas the SADP from the [011]bcc is shown on the top right of the image as the inset. The presence of the super-lattice spots in the [011]bcc (highlighted by yellow circle in the inset image) clearly establishes that the chemical ordering in this region is still present after deformation. The bcc/B2 phase in AlXCoCrFeNi has been reported to be much stronger compared to the fcc phase1. Liao et al. used transmission electron microscopy (TEM) on an fcc/B2 eutectic alloy, that the plastic deformation essentially took place in the softer fcc phase with nanohardness of 2.7 GPa and few dislocations were seen in the harder B2 phase with nanohardness of 4.4 GPa11. The fcc phase deforms first resulting into strain mismatches at interfaces and heterogeneous deformation-fields. That can in turn result in accumulation internal stresses accommodated by larger storage of geometrically-necessary-dislocations (GND) at these interfaces28. The interfaces can act as the barriers to dislocation-motion30. The post-test microstructures in Fig. 7(c) shows a heavy pile-up of dislocations in the softer fcc phase at the fcc-B2 interface. The fine-scale lamellae sizes would elevate twinning stress and retard twinning25. Due to high twinning stresses, phenomena like dislocation locking have been reported to be dominant30. These barriers can increase with tendency for slip planarity due to relatively low SFE, high Peierls-Nabarro stresses, and ordered phases (in the case of CR-H-580).

There is no clear evidence of large-scale twinning in any of the two regions. However, on examination at a higher magnification in HRTEM mode, fine scale faults/nano-twins are observed as shown in Fig. 7(d,e). Figure 7(d) shows the HRTEM of nano-twins along [011]fcc in the CR-H condition after quasi-static testing to failure. Fourier filtered image in Fig. 7(e) depicts the atomic resolution of the fine-scale, few atomic planes thick twins. The corresponding Fourier filter transform (FFT) is shown as an inset. This condition shows high density of nano-twins but no thicker twins are observed. The elemental composition of fcc phase is comparable to ~Al0.1CoCrFeNi (refer Supplementary Table T1). Choudhuri et al. investigated Al0.1CoCrFeNi alloy and reported nano-scale twinning in the alloy after quasi-static deformation, the deformation behavior of the fcc phase in the current alloy can be compared to that31. The high work hardening behavior of the current alloy can be due to the high density of nano-twins and large dislocation accommodation at the long range obstacles in form of fcc-B2 interfaces.

Now we present the TEM results from the dynamically deformed (strain rate = 2 × 103) CR-H sample. Figure 8(a) shows a low magnification BFTEM image showing the fcc and bcc regions as labeled in the figure. A stark difference here on comparison to the quasi-static condition is the high density of twins in the fcc region. The SADP taken from the fcc region is shown as the inset to the Fig. 8(a) and that from the bcc/B2 region is shown in Fig. 8(b). The bcc/B2 region has highly faulted structure as can be seen in Fig. 8(c). A high magnification image showing the twins in the fcc phase is shown in Fig. 8(d). The twin thickness is about 20 nm which is much thicker compared to deformation under quasi-static testing.

Investigation on CR-H-580 sample after deformation is shown in Supplementary Fig. S3. Figure S3(a,b) show results from the quasi-static testing and Fig. S3(c) shows the results from the dynamically tested sample. Note, the super-lattice spots, in the ZA = [011]fcc SADP shown in the inset of Fig. S3(a) after quasi static testing and in ZA = [112]fcc SADP shown as the bottom inset of Fig. S3(c) after dynamic testing, are absent. Hence, the L12 phase disorders after deformation under both strain rates. Dissolution of L12 on deformation has been discussed in literature both in superalloys as well as in HEAs16,32. The L12 disorders when the dislocations shear through them and form anti-phase boundaries. The anti-phase boundaries can further increase the strain hardening rate of the alloy. An increase in the strain hardening rate (refer Fig. 6(b)) can be explained by disordering of L12 precipitates and formation of anti-phase boundaries. Wani et al.16 suggested that microbands and shear bands could be involved in the disordering process.

Comparing the propensity of twinning under the two different deformation rates, the twinning increases sharply under high strain rate testing as seen in Fig. S3(c). The B2 region remains ordered as seen in the ZA = [011]bcc SADP which shows presence of the super-lattice spots in the top inset of the Fig. S3(c). Deformation in the fcc phase can be explained by collective dislocation glide and nucleation governed plasticity while that of the B2 phase is due to dislocation cross-slip. This is further investigated by TEM analysis to show the twinning elements in fcc at high strain rate.

## Conclusions and Summary

The effect of thermo-mechanical treatment on phase evolution and mechanical properties in an fcc-based Al0.7CoCrFeNi HEA was investigated. While the dual phase eutectic Al0.7CoCrFeNi was precipitation strengthenable by introducing hard-coherent intermetallic phase in the fcc phase via suitable heat treatment, post deformation TEM examination was used to investigate the modes of deformation under various strain rates. The following can be established from the current study:

1. (1)

Phase composition

The alloy was cast, homogenized, rolled and heat treated at two different temperatures i.e. 1100 °C and 580 °C. It was observed that the even on water quenching (fast cooling) from 1100 °C(CR-H condition), the B2 to B2 + bcc transformation in the B2 lamellae takes place. However, fcc phase can be retained as disordered in CR-H condition. Another heat treatment was conducted on the CR-H condition by annealing the alloy at 580 °C for 24 h. This heat treatment introduced nano-scale L12 precipitates in the fcc lamellae. APT results revealed the compositions of the fcc, L12, B2 and bcc phases.

2. (2)

Mechanical testing

The alloy was tested under quasi-static (strain rate = 10−3) tensile loading and dynamic (strain rate = 2 × 103) compressive loading. Introduction of a large density of coherent nano-scale L12 precipitates in the fcc phase resulted in significant YS increase in the alloy. The fcc & L12 + B2 & bcc microstructure exhibited an yield strength of ~1000 MPa, ultimate tensile strength (UTS) of ~1400 MPa and elongation to failure of ~13% under quasi-static loading whereas flow stresses ~1800 MPa under dynamic loading. The strengthening contribution due to fine scale L12 is modeled using Orowan dislocation bowing and by-pass mechanism.

L12 precipitates disorders on deformation under both quasi-static and high strain rate. Post deformation transmission electron microscopy analysis revealed that twinning is observed in fcc phase under high strain rate deformation, which was minimal under quasi-static loading.

3. (3)

Work hardening rate

Drawing from the work hardening plot (Fig. 6(b), the alloy is expected to show immense propensity to deformation twinning, but after post deformation examination such is not observed. Despite of low deformation twinning seen after quasi-static testing, the high work hardening in the CR-H condition could be due to higher dislocation storage capacity at the interfaces and dislocation locking mechanism. In CR-H-580 under quasi-static testing the disordering of L12 phase resulting in formation of anti-phase domains can further increase the strain hardening in the alloy.

4. (4)

Strain rate sensitivity (SRS)

Even though fine-scale L12 precipitates increased strength by 30% in aged CR-H-580, they are coherent in nature and thermally activated. So SRS drops only slightly in this microstructure. The precipitate free channel near the interface of the B2 + bcc and fcc + L12 lamellae (refer Fig. 5) can be relatively softer as compared to the fcc + L12 regions, and consequently act as sites for high dislocation storage in the vicinity of the interfaces during deformation. Such a mechanism could also potentially rationalize the similar strain rate sensitivity observed in case of the Al0.7CoCrFeNi eutectic HEA, in the absence or in the presence of L12 precipitates within the fcc-based lamellae.

## Data Availability

All the background data and information is available with the corresponding author and can be presented on a reasonable request.

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## Acknowledgements

This research was done as a part of cooperative agreement between the Army Research Laboratory and the University of North Texas (W911NF-16-2-0189).

## Author information

B.G. conceptualized the idea, conducted the SEM, TEM, APT analysis and quasi-static tensile deformation, S.G. conducted the high strain rate compressive deformation tests, Y.Z. conducted the STEM EDS, V.S. conducted the EDS and EBSD experiments. R.S.M. and R.B. guided throughout the research. B.G. and R.B. wrote the manuscript.

Correspondence to Rajarshi Banerjee.

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• ### Dynamic tensile deformation and microstructural evolution of AlxCrMnFeCoNi high-entropy alloys

• C.M. Cao
• , W. Tong
• , S.H. Bukhari
• , J. Xu
• , Y.X. Hao
• , P. Gu
• , H. Hao
•  & L.M. Peng

Materials Science and Engineering: A (2019)