Effect of Multistage High Temperature Thermomechanical Treatment on the Microstructure and Mechanical Properties of Austenitic Reactor Steel

Abstract

The deformation microstructures formed by novel multistage high-temperature thermomechanical treatment (HTMT) and their effect on the mechanical properties of austenitic reactor steel are investigated. It is shown that HTMT with plastic deformation at the temperature decreasing in each stage (1100, 900, and 600 °C with a total strain degree of e = 2) is an effective method for refining the grain structure and increasing the strength of the reactor steel. The structural features of grains, grain boundaries and defective substructure of the steel are studied in two sections (in planes perpendicular to the transverse direction and perpendicular to the normal direction) by Scanning Electron Microscopy with Electron Back-Scatter Diffraction (SEM EBSD) and Transmission Electron Microscopy (TEM). After the multistage HTMT, a fragmented structure is formed with grains elongated along the rolling direction and flattened in the rolling plane. The average grain size decreases from 19.3 µm (for the state after solution treatment) to 1.8 µm. A high density of low-angle boundaries (up to ≈ 80%) is found inside deformed grains. An additional cold deformation (e = 0.3) after the multistage HTMT promotes mechanical twinning within fragmented grains and subgrains. The resulting structural states provide high strength properties of steel: the yield strength increases up to 910 MPa (at 20 °C) and up to 580 MPa (at 650 °C), which is 4.6 and 6.1 times higher than that in the state after solution treatment (ST), respectively. The formation of deformed substructure and the influence of dynamic strain aging at an elevated tensile temperature on the mechanical properties of the steel are discussed. Based on the results obtained, the multistage HTMT used in this study can be applied for increasing the strength of austenitic steels.

1. Introduction

Austenitic stainless steels are used as structural materials in various industries, including the nuclear power engineering [1,2,3]. In Russia, austenitic stainless steels ChS-68 (Fe-16Cr-15Ni-2Mo-Mn-Ti-V-B) and EK-164 (Fe-16Cr-19Ni-2Mo-2Mn-Nb-Ti-B) are used for the manufacture of fuel cladding shells of fast-neutron (Generation III) nuclear reactors BN-600 and BN-800 [4,5,6]. These steels have a number of attractive qualities, such as high ductility, increased heat resistance, lack of tendency to low-temperature embrittlement compared to other structural materials. A common problem limiting the use of austenitic steels in the nuclear power industry is their radiation-stimulated swelling at high irradiation doses. The studies of radiation porosity under irradiation in the BN-600 reactor (maximum damaging dose 77 dpa) [5,6] showed that under identical irradiation conditions, steel EK-164 swells 1.5–2 times less than steel ChS-68. Some authors [5] attribute this to the increased content of Ni (19% wt.) and the complex system of alloying—the presence of Ti, Nb, V, B, Si, etc. It was shown [5] that austenitic steel EK-164 is a radiation-resistant material ensuring fuel burn-up of over 15%. At higher irradiation doses (more than 100 dpa) and higher fuel burnout, EK-164 and ChS-68 steels swell significantly, which limits their applications in nuclear power engineering.

Radiation swelling is affected by several factors [7]: solid-solution, dislocation and phase stability. The solid-solution influence is determined by the concentration of the alloying elements (primarily Ni) and C, V, Ti, Nb, Si, B in the solid solution. The second factor is determined by the substructure formed as a result of plastic deformation. The increased density of dislocation sinks for point defects inhibits the formation of pores under irradiation conditions. The phase stability of austenite determines the formation of precipitates, their compositions, volume fractions, location and morphology. These factors are interrelated with each other and determine the processes of pore nucleation and growth [7]. Optimization of these factors makes it possible to study the use of austenitic steels at higher (over 100 dpa) damaging irradiation doses.

Currently, cold rolling deformation (up to 20–30%) is applied to form the substructure in austenitic steels used as shells of fuel elements [5]. This substructure is characterized by deformation twins and increased dislocation density (relative to solid solution treatment). These features of the microstructure of austenitic reactor steels determine the required long-term high-temperature strength properties and radiation resistance. An increase in the degree of cold deformation contributes to a more intensive deformation twinning with the formation of a high density of microtwin packets, which significantly reduces the ductility of steels [8,9]. The possibilities of thermomechanical treatments using hot and warm deformation to form the substructure and increase the mechanical properties in austenitic reactor steels have been little studied.

Previously, the possibility of improving mechanical properties and modifying the microstructure under conditions of HTMTs was shown on such austenitic steels as AISI 304 [10,11], 310 [12], 316 [13] and 321 [11,14,15]. Most of these works, focus on the formation of dynamic recrystallization (DRX) grains; the main methods for their formation are HTMT with hot rolling [13,16] or compression [12,17,18] with degrees of deformation e = 0.7–3 in the temperature range of 800–1200 °C. These treatments promote an intensive formation of DRX grains at high temperatures of 900–1200 °C. In this case, a higher deformation temperature more strongly promotes the growth of DRX grains and an increase in the volume fraction of DRX [17]. Consequently, a similar structure formed by HTMT at high temperatures strengthens the steels but only slightly.

For example, in [13] the effect of warm plastic deformation in the temperature range of 500–900 °C with a total strain degree of e = 2 on the microstructure and mechanical properties of austenitic steel AISI 316 is investigated. It was shown that these thermomechanical treatments lead to the development of grain fragmentation, an increase in the dislocation density, and the formation of DRX grains. It was noted that the lower was the plastic deformation temperature, the more fragmented and elongated grains were formed in the rolling direction. In addition, at low temperatures (below 600 °C), the DRX processes are suppressed [13]. As a result, higher values of mechanical properties were achieved at a deformation temperature of 500 °C: yield strength of 945 MPa, elongation to failure of 10.5%.

In [15], the effect of hot deformation at 1100 °C (e = 1.6), and a sequence of hot deformation at 1100 °C (e = 0.8) and warm deformation at 600 °C (e = 0.7) on the microstructure and mechanical properties of 321 type austenitic steel is demonstrated. It is shown that HTMT, with decreasing temperature in the sequence of treatments, causes a high-intensity fragmentation of the steel structure and has a positive effect on the strength properties (yield strength of 677 MPa) while maintaining acceptable plasticity (elongation to fracture 12%).

The effect of HTMTs (including multistage HTMTs) on the microstructure features and mechanical properties of reactor-grade steels (type EK-164) has not been studied before.

In this paper, the effect of high-temperature thermomechanical treatment consisting of a sequence of plastic deformations with a decrease of temperature (hot, warm deformation—multistage HTMT) on the microstructure and mechanical properties of austenitic reactor steel EK-164 is studied.

2. Materials and Methods

The material used in this study was a Russian grade austenitic reactor steel EK-164, the chemical composition of which is presented in

Table 1. Chemical composition of the austenitic reactor steel EK-164 (wt. %).

Fe	Ni	Cr	Mo	Mn	Si	Ti	Nb	V	C
bal.	17.92	15.93	2.4	1.74	0.68	0.4	0.28	0.12	0.07

. Prior to deformation, the samples were solution treated (ST) at 1100 °C for 1 h followed by water quenching (Figure 1). Heating was carried out in a tubular electric furnace of the T-40/600 type (Plant “LETO”, Tula, Russia). The temperature was determined by the furnace thermocouple. The rolling mill was maintained at room temperature. The initial samples size was ≈ 54 × 11 × 11 mm³.

HTMT consisted of a sequence of hot (HR) and warm (WR) plastic deformations by rolling. The first stage of processing consisted of plastic deformation to a strain degree of e = 0.7 in 1 pass with preheating to 1100 °C (HTMT-1). The thickness of the samples after HTMT-1 decreased down to ≈ 5.5 mm. The second stage of processing included HTMT-1 and subsequent plastic deformation to a strain degree of e = 0.7 in 1 pass with preheating to 900 °C (HTMT-2). The thickness of the samples after HTMT-2 was ≈ 2.7 mm. The third stage of treatment included HTMT-2 and subsequent rolling deformation in 2 passes with a total strain degree of e = 0.6 (the thickness of the samples ≈ 1.6 mm) with preheating to 600 °C (HTMT-3). The exposure of the samples in the furnace to these specified temperatures was 10 min. The time between the removal of the samples from the furnace and the start of plastic deformation was about 3–5 s. After removal from the mill the samples were immediately quenched in water. After HTMT-3, cold deformation (CR) was performed at 20 °C in 5 passes with a total strain degree of e = 0.3 (HTMT-3 + CR). The final thickness of the samples after thermomechanical treatments was ≈ 1.15 mm.

The microstructural characterization was performed using a Tescan MIRA 3 LMU Field Emission scanning electron microscope (FE SEM) equipped with a Field Emission Gun (TESCAN ORSAY HOLDING, Brno, Czech Republic) and an Oxford Instruments Nordlys F electron backscatter diffraction detector (Oxford Instruments, High Wycombe, UK). The SEM EBSD samples were prepared by standard metallographic techniques: sandpaper grinding to #2000, diamond polishing 9 to 1 µm, 50 nm col-K suspension fine polishing. The final stage was ion milling for 25 min at 10 kV. Ion polishing was performed using a Technoorg Linda SEMPrep 2 system (Technoorg Linda Co. Ltd, Budapest, Hungary). The EBSD images were taken from the longitudinal (perpendicular to transverse direction—TD) and parallel to the rolling plane (perpendicular to normal direction—ND) sections. Further, these sections are designated as perpendicular to TD and ND, respectively. The EBSD data for ST samples were obtained with step sizes of 200 and 125 nm for the areas of 250 and 50 µm², respectively. After HTMT-3 the step size for these areas was 200 and 50 nm, respectively. The microstructure was examined by the Oxford Instruments AZtec software (version 3.1, Oxford Instruments, High Wycombe, UK).

TEM and scanning TEM (STEM) investigations were conducted using the Philips CM-12 (FEI Company, Hillsboro, OR, USA) and JEOL JEM-2100 electron microscopes (JEOL Ltd., Akishimam Tokio, Japan) at an accelerating voltage of 120 kV and 200 kV, respectively. Thin foils were prepared from the sections perpendicular to TD by electropolishing in an electrolyte containing 450 mL of orthophosphoric acid and 50 g of chromic anhydride.

Mechanical tests were carried out at room temperature (20 °C) and at high temperature close to the maximum nuclear reactor operating temperature (650 °C) by the method of static tensile deformation at a strain rate of ≈ 2 × 10⁻³ s⁻¹ on a NIKIMT 1246R-2/2300 high-temperature vacuum testing machine (Experimental Plant “NIKIMP” (Research and Design Institute of Testing Machines, Instruments and Measuring Instruments), Moscow, Russia) using dog-bone samples with the gage length of 13 mm and gage section of 2 × 1 mm². Samples were cut from section parallel to the rolling plane. Tension was performed in the rolling direction. High temperature tensile tests were carried out in a vacuum of ≈ 2.5–3.5 × 10⁻⁵ Pa.

3. Results

3.1. SEM EBSD and TEM Studies of Deformed Microstructure

The results of the structure investigation of EK-164 steel in the ST state are presented in Figure 2. The phase map (Figure 2a) shows that the microstructure consists of austenite with the average grain size of ≈19.3 μm. An analysis of the grain boundaries shown in Figure 2a and the distribution of grain misorientations shown in Figure 2c suggests that the samples contain a high fraction of special type boundaries. The histogram of the grain distribution by the misorientation angles shows a pronounced peak near 60° (Figure 2c). This peak corresponds to the annealing twins. The fraction of the special type Σ3 boundaries (twin boundaries) is 68.2%. At the same time, the fraction of high-angle boundaries is 97% and that of low-angle boundaries—3%. Taking into account the annealing twins, the average grain size is ≈7.7 μm (Figure 2d).

It should be noted that annealing twins are found in the grains with the widths of several microns (Figure 2a,b) and those narrower than 1 μm (Figure 2e,f). In addition, coarse (up to several µm) particles of the MX type (where M—Nb, Ti or V; X—C) (Figure 2e,f) were found inside austenite grains. The volume fraction of these particles does not exceed 1%. Earlier [19], it was shown by TEM that fine (from several nm to 50 nm) MX particles based on vanadium were also observed in the structure of steel EK-164. These particles are not identified by EBSD methods due to their small size.

Thin foils in the sections perpendicular to TD were studied by TEM methods. It was shown that HTMT-1 leads to the grain fragmentation and the formation of numerous new low-angle boundaries. As a result, the plates with curved boundaries, which are elongated in the rolling direction, are formed inside the austenitic grains (Figure 3a). Their widths can be up to several microns. The plates have low-angle misorientation boundaries (Figure 3b). It should be noted that in some areas of the microstructure, there are regions with predominantly equiaxed subgrains with dimensions of ≈1 µm (Figure 3c). In addition, accumulations of MX-type particles were detected in these areas.

HTMT-2 contributes to an increase in the dislocation density inside the fragmented plates (Figure 4a). An analysis of the diffraction pattern reveals the presence of low-angle and high-angle misorientation boundaries between the fragmented plates (Figure 4b). In addition, the diffraction pattern contains low- and high-angle misorientation boundaries between the fragmented plates (Figure 4b). The presence of the latter is evidenced by the presence in the diffraction pattern of two zone axes of [110] and [001], the misorientation between them being as large as 45°. Figure 4c shows a typical microstructure consisting of several plates with high- and low-angle misorientation boundaries. In the center, there is a plate with a width of ≈1.5 microns with an internal subgrain structure having low-angle misorientation boundaries. On the left and right, this plate has high-angle misorientation boundaries with thinner plates (wide ≈ 400–500 nm). Fine particles of the MX type were found in the grain volume.

The microstructure of steel after HTMT-3 in two sections perpendicular to TD and ND was investigated by EBSD methods. It has been shown that HTMT-3 leads to significant grain refinement in the section perpendicular to TD (Figure 5a). The average grain size is ≈1.8 µm. Austenitic grains have a specific shape—elongated plates. Their length can reach ≈100 µm. On the phase map among the fragmented plates, individual large particles of the MX type can be seen (Figure 5b). The fraction of special type Σ3 boundaries (annealing twins) decreases to less than 1%. This is due to the high (e = 2) strain degree at the elevated temperatures. In this case, the initial boundaries of the annealing twins become the arbitrary type boundaries. The fraction of high-angle boundaries is ≈44.8%, and that of low-angle boundaries is ≈55.2% (Figure 5c). The histogram of grain size distribution (Figure 5d) shows that the structure mainly contains grains up to 5 µm in size, but there are also individual grains of ≈20 µm. It should be noted that the fine grains are located along the elongated coarse grains (Figure 5a). In the images with high magnification (Figure 5e,f) MX particles with a size of ≤1 µm were detected. They are located mainly along the grain boundaries.

After HTMT-3, in the section perpendicular to ND, the fragmented microstructure consists of grains with sizes of tens of micrometers and grains with sizes up to 5 μm (Figure 6a). The volume fraction of these grains is 5 and 95%, respectively. The average grain size (as in the section perpendicular to TD) is ≈1.8 μm. At the same time, coarse grains (up to 74 μm) were found, the dimensions of which exceed the maximum size in the ST state. This is due to the flattened shape of the grains in the rolling plane and elongated shape in the rolling direction. Multiple low-angle boundaries (Figure 6b) and clusters of fine grains (up to 5 μm) were found inside the coarse grains. The histogram of the grain misorientation distribution (Figure 6c) shows that the fraction of high-angle boundaries decreases (down to 19.8%) and that of low-angle ones increases (up to 80.2%) compared to the section perpendicular to TD.

It is shown by TEM that after HTMT-3 in the section perpendicular to TD the minimum width of the elongated plates is less than 200 nm. Between the plates (Figure 7a) both low-angle and high-angle misorientation boundaries are observed. This follows from the analysis of the SAED pattern, which shows two axes of the zone [110]γ with a misorientation of 60° (Figure 7b).

The subsequent cold deformation (after HTMT-3) leads to intensive mechanical twinning. STEM techniques show that deformation microtwins are formed in a significant volume of the material, including the fragmented plates (Figure 8a). Many fragmented plates are filled by nanotwin packets (Figure 8b). Note that low-angle boundaries are not obstacles for microtwins propagation (Figure 8c). Microtwins in these plates are observed on several twinning planes. A characteristic azimuthal twisting of the reflections (Figure 8d) was detected on the corresponding SAED pattern. This is due to the numerous low-angle misorientation boundaries resulting from HTMT-3 + CR. In addition, there are extended reflections in diffraction patterns due to the presence of thin nanoscale twin plates (Figure 8c). No mechanical twinning is detected in plates narrower than 100 nm. Basically, such plates lie between wide plates with an internally twinned structure.

It should be noted that the formation of new MX particles during multistage HTMT was not detected by structural investigations.

3.2. Mechanical Properties

The results of investigation of the steel mechanical properties in the ST state and after each HTMT stage are presented in

Table 2. Mechanical Properties of EK-164 Steel.

Treatment	Temp. Tensile Tests, °C	YS, MPa	TS, MPa	El., %
ST	20 650	201.4 ± 2 95 ± 6.3	539.2 ± 9.6 360.2 ± 8.8	47.4 ± 0.1 31 ± 1.6
HTMT-1	20 650	425.8 ± 16.8 297.3 ± 42.7	598 ± 0.4 431.3 ± 5.9	23.4 ± 0.7 16.3 ± 4.1
HTMT-2	20 650	642.9 ± 21.1 472.7 ± 22.3	731.5 ± 16.8 522.2 ± 1.6	11.4 ± 1.1 4.5 ± 1
HTMT-3	20 650	764.8 ± 1.6 521 ± 17.7	859.9 ± 12.2 589.8 ± 39.3	7.8 ± 0.4 4.8 ± 0.7
HTMT-3 + CR	20 650	911.9 ± 25 580.2 ± 5.2	1041.4 ± 34.7 706.5 ± 39.9	5.4 ± 0.6 6.1 ± 2.1

and Figure 9. In the ST state at 20 °C, characteristic mechanical properties for austenitic steel are observed (Table 2). At an elevated tensile temperature (650 °C) in this state, the yield strength is ≈95 MPa, the elongation to fracture is ≈31%. HTMT-1 leads to an increase in strength—the yield strength increases by ≈225 MPa (at 20 °C) and ≈200 MPa (at 650 °C). In this case, the elongation to fracture decreases by a factor of 2 both at 20 °C and 650 °C. Subsequent HTMT-2 and HTMT-3 contribute to a further strengthening of the steel—the yield strength increases up to 765 MPa (at 20 C) and up to 520 MPa (at 650 °C). An increase in strength properties is accompanied by a decrease in the values of elongation to failure—to 7.8% and 4.5%, respectively (Table 2). These changes in the mechanical properties are associated with the formation of elongated and flattened austenite grains, the average size of which decreases by a factor of 4.3 compared to the ST state. In addition, note that the resulting fragmented structure with numerous low-angle misorientation boundaries (up to ≈ 80% in the section perpendicular to ND) plays a key role in strengthening of the material.

Cold deformation after HTMT-3 due to the development of multiple twinning inside the fragmented plates contributes to additional steel strengthening. The above microstructure provides the maximum values of strength properties both at a tensile temperature of 20 °C (yield strength ≈ 910 MPa) and at 650 °C (yield strength ≈ 580 MPa). The retention of high values of strength properties at an elevated tensile temperature is associated with the high thermal stability of deformation twins. According to the in-situ studies [20], microtwins are capable of surviving in the structure of austenitic steels up to 1000 °C with a holding time of up to 37 min. The high density of microtwins after HTMT-3 + CR contributes to a significant decrease in the elongation to failure down to ≈5–6%.

Strain curves at 20 °C in the ST state, as well as after HTMTs, are monotonic without any features (Figure 9a). Thermomechanical treatments lead to an increase in the tensile strength and yield strength and a decrease in the plastic properties. At elevated tensile temperature (650 °C) in the ST state, as well as after HTMT-1 and HTMT-2, regions with serrated plastic flow were found in the curves (Figure 9b). In the ST state and after HTMT-1, these regions are observed practically along the entire length of the flow curves. These features of the curves are associated with the dynamic strain aging (DSA). After HTMT-2, this phenomenon is observed on a narrow segment of the curve. The increase in the yield and tensile strengths at high temperatures after HTMT-3 relative to HTMT-2 is insignificant (∆σ ≈ 50–70 MPa) compared to similar values at 20 °C. No serrated flow is detected after HTMT-3. In addition, the elongation to failure after these treatments decreases down to ≈ 5%, which is comparable to the corresponding value after additional cold deformation (Figure 9). These features indicate the suppression of DSA in severely deformed structural states.

4. Discussion

4.1. Grain Refinement and Substructure Formation

Microstructural evolution of EK-164 steel under multistage HTMT (total strain of e ≈ 2) is typical for fcc steels with low and medium stacking fault energies, deformed at different temperatures [13,14,21]. With an increase in the degree of deformation the dislocation density increases, and new low- and high-angle misorientation boundaries are formed. Hot and warm rolling deformation promotes fragmentation and a change of the shapes of austenite grains. With a decrease in the deformation temperature, the fragmentation of grains occurs more intensively, as in [13,22]. As a result, during HTMT, the initial equiaxed grains become elongated in the rolling direction (Figure 5) and flattened in the rolling plane (Figure 6). This microstructure is called pancake grain structure or pancaked grains [12,21]. Fine grains are found in the volume of large coarse grains and along their boundaries (Figure 6b). It is shown by Belyakov A. et al. [13,22,23] and Huang L. et al. [24,25] that under thermomechanical treatments in the temperature range of 500–1100 °C at high strain rates and degrees (e ≥ 2) DRX develops in austenitic steels. It is noted that at higher deformation temperatures, the formation of DRX grains occurs more intensively. In this work, the formation of DRX grains is suppressed, since warm deformation (HTMT-3), that completes the HTMT sequence, occurs at a temperature much lower than that required for the nucleation of DRX grains. It is assumed that the formation of fine grains is associated with deformation grain refinement due to a high total strain degree. Subsequent cold deformation (e = 0.3) promotes additional fragmentation of the structure due to mechanical twinning. At low deformation temperatures in austenitic steels with low and medium stacking fault energies, mechanical twinning is a deformation mechanism competing with the dislocation slip [9,20,26]. As a result, a high density of deformation micro- and nanotwins is formed inside the elongated grains.

4.2. Comparison of Mechanical Properties

It should be noted that the achieved mechanical properties of EK-164 steel after multistage HTMT are comparable with the properties presented in [13,15] on other austenitic steels. It is shown [13] that the yield strength reaches 875 MPa (at 20 °C), 580 MPa (at 600 °C), and 430 MPa (at 700 °C) after HTMT with plastic deformation at 700 °C with a total strain degree of e = 2. At this deformation temperature, DRX is realized in steel. In this case, the elongation to failure decreases (from 10 to 5%) with a change in the tensile temperature from 20 to 700 °C. The authors note that DSA is not observed in this case. In [15], HTMT with a sequence of hot and warm deformation (total deformation e ≈ 1.5) leads to an increase in the yield strength up to 677 MPa, while maintaining the elongation to fracture ≈ 12% at 20 °C.

In the present study, the values of the yield strength achieved after HTMT-3 are close to those indicated in [13] and are significantly higher than that in [15]. The latter is associated with a lower degree of deformation and, as a consequence, less fragmented substructure.

4.3. Dynamic Strain Aging during Tensile Tests at 650 °C

The phenomenon of dynamic strain aging consists in the precipitation of dispersed particles during deformation at elevated temperatures and is a consequence of the interaction between the solute atoms and the movable dislocations during tensile plastic deformation [27,28,29]. This phenomenon is also called the Portevin–Le Chatelier effect. It is known that DSA develops in the structure due to the generation of new dislocations that are involved in the deformation process. Such dislocations move until they encounter with impurity atoms. This is accompanied by blocking of dislocations and an increase in tensile stresses, which contributes to the nucleation of new dislocations. As soon as there are enough new dislocations, the process of further plastic flow starts. As a result, serrations are formed on the flow curve.

The main factors affecting DSA are strain rate, temperature, chemical composition, etc. [27,28,29] Figure 9b shows that a serrated flow is observed on some tensile curves at elevated test temperatures. This type of serrations, which are characterized by a sharp increase in stress, alternating with a plateau, is referred to as type A serration, according to the classification of Rodriguez [30]. This behavior is associated with tension at a relatively high strain rate ≈ 2×10⁻³ s⁻¹. Earlier [31], it was shown that tensile tests of EK-164 steel samples in the ST state leads to the development of DSA processes in the temperature range of 400–650 °C. At the same time, with an increase in the deformation temperature, the density and intensity of the peaks on the tensile curves increase. In [12] it was shown on AISI 310 steel under tension in the temperature range of 800–1100 °C that during DSA complex carbides are formed (based on Cr, Mo, Ni, Fe) located along grain boundaries. Sun H. et al. [12] argue that precipitation is caused by the effect of the applied stress.

In the present work, in the ST state and after HTMTs, the DSA effect is observed on the tensile curves at 650 °C, from the very beginning of plastic flow. The difference in these curves is that after HTMT-1 there is a section with a stress drop (Figure 9c), during which the dislocation motion is unblocked. The high-angle misorientation boundaries created during processing serve as barriers to the dislocation motion, and with an increase in the density of these boundaries, the DSA effect is suppressed. After HTMT-2, the DSA effect on the stress-strain curve is observed only in the stage of neck formation and is short. In this state, the density of dislocations and low- and high-angle boundaries is higher and, therefore, the number of barriers to the motion of movable dislocations becomes larger. As a result, the plastic part of the flow curve is significantly reduced. No DSA effect is detected after HTMT-3 and HTMT-3 + CR for the same reason. Thus, the deformation structure and substructure formed during HTMTs have a decisive influence on the development of DSA processes during tensile testing of EK-164 steel.

5. Conclusions

In this paper, the effect of multistage HTMT with plastic deformation with the temperature decreasing in each stage (1100, 900, and 600 °C with a total strain degree of e = 2) on the microstructure and mechanical properties of the EK-164 austenitic reactor steel has been investigated. The main results can be summarized as follows:

• Under HTMTs, structural states with the pancake grain structure are formed, which is characterized by grains elongated in the rolling direction and flattened in the rolling plane. The average grain size is 1.8 μm, which is 10.7 μm less than in the ST. A high density of low-angle boundaries up to ≈ 80% (in the section perpendicular to ND) and up to ≈55% (in the section perpendicular to TD) was found inside the fragmented grains.
• Additional cold deformation with e = 0.3 (after HTMTs) allows the creation of a high density of micro- and nanotwins of deformation in fragmented grains. Low-angle boundaries are not obstacles for microtwins propagation. At the same time, coarse and finely dispersed particles of the MX type are preserved without their additional precipitation after all treatments.
• The tensile tests at a strain rate of~10⁻³ s⁻¹ showed that the obtained microstructure provides high strength properties of steel: yield strength ≈ 580 MPa and 910 MPa, tensile strength ≈ 700 MPa and 1040 MPa at 650 °C and 20 °C, respectively.
• At elevated tensile temperatures, serrated flow is observed on the curves due to the DSA effect. The high density of low and high angle boundaries formed as a result of HTMT-3 and HTMT-3 + CR inhibits the dislocation motion and suppresses the DSA effect during tensile tests.

Thus, multistage HTMT (with a total strain degree of e ≈ 2.3) is an effective method for forming a deformed substructure and increasing the strength of the austenitic reactor steel.