Recent progress and future research prospects on the plastic instability of medium-Mn steels: a review
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摘要: 中錳鋼是近年來出現的新型鋼鐵材料，因為其優異的力學性能被認為是第三代汽車用鋼，但是該鋼的一個突出特點就是在拉伸變形時會發生塑性失穩，導致材料結構穩定性減弱甚至在某些情況下過早失效，這已然成為限制中錳鋼商業化使用的關鍵問題。塑性失穩包括出現不連續屈服和屈服平臺（呂德斯應變）以及流變應力鋸齒（PLC效應）。兩者都受到成分、晶粒形貌、退火工藝、組織構成等因素的影響，也均與拉伸變形過程中 奧氏體相變轉變存在或強或弱的相關性，使得這一塑性失穩現象的機理更為復雜化，因而在近期各種觀點迥異的理論解釋也相繼被提出。本文綜述了相關研究中各種因素對呂德斯應變和PLC效應的影響結果及相關理論解釋，并著重指出了各理論解釋的局限性及未來的研究思路。最后，基于現有研究和預研實驗對在保證中錳鋼超高強度和優良塑性的前提下消除中錳鋼塑性失穩現象的可行途徑進行了展望。Abstract: Lightweight materials are desired for energy saving and emission reduction of automobiles. A promising material for automobile parts is advanced high strength steel (AHSS). A recently developed material called medium-Mn steel, with excellent mechanical properties, has attracted increasing attention as the third-generation AHSS for automotive processing. However, medium-Mn steel is disadvantaged by plastic instability during tensile tests. This plastic instability is usually associated with localized and propagative bands on the material surface, which cause an unexpected surface roughening effect and premature failure in the most unfavorable cases. Therefore, plastic instability has severely impeded the commercialization of medium-Mn steels. The phenomenon manifests as discontinuous yielding followed by a yielding plateau (the Lüders strain), along with flow stress serrations (the Portevin-Le Chatelier (PLC) effect). Both effects are influenced by the composition, annealing process, and microstructure (phase morphology and constituents) of the steel. Both effects are also correlated with the austenite-to-martensite transformation during deformation to a greater or lesser extent, which is rarely observed in metallic materials. Consequently, the mechanisms of both effects are complicated and explainable by diverse theories. This paper reviewed the current research results on the influences of various factors on the Lüders strain and PLC effect, and discussed their corresponding mechanisms. This paper particularly emphasized the limitations of the existing theoretical explanations and proposed future researches to elucidate the existing disputes. Based on the current research and our preliminary experiment, this paper finally suggested ways of eliminating the plastic instability of medium-Mn steel, while guaranteeing ultrahigh strength, and excellent ductility. These improvements will drive the future development of this field.
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圖 1 馬氏體和冷軋板初始組織在不同溫度臨界退火后的應力?應變曲線.（a） 0.1%C?5%Mn鋼；（b） 圖(a)屈服平臺放大圖；（c） 0.2%C?5%Mn鋼；（d） 圖(c)屈服平臺放大圖[16]
Figure 1. Engineer stress?strain curves of martensitic and cold rolled initial structures for steels after intercritical annealing at various temperatures: (a) 0.1%C?5%Mn steel; (b) the magnification views of the yield plateau in (a); (c) 0.2%C?5%Mn steel; (d) the magnification views of the yield plateau in (c)[16]
圖 2 Fe?0.055%C?5.6%Mn?0.49%Si?2.2%Al鋼冷軋板在不同制度退火后的工程應力?應變曲線和變形過程中奧氏體體積分數的變化. （a） 700 ℃退火10 min；（b） 740 ℃退火10 min[18]
Figure 2. Engineer stress?strain curves and the changing of austenite volume fraction during deformation for the cold rolled sheet of Fe?0.055%C?5.6%Mn?0.49%Si?2.2%Al steel after annealing at various temperatures: (a) annealed at 700 ℃ for 10 min; (b) annealed at 740 ℃ for 10 min[18]
圖 3 Fe?7.5%Mn?1.5%Al?0.2%C鋼冷軋板在650 ℃和665 ℃退火后的拉伸應力?應變曲線（a），拉伸實驗前后的奧氏體體積分數（b），以及呂德斯帶傳播前后奧氏體的轉變量（c）[22]
Figure 3. Stress?strain curves of the cold rolled sheet for Fe?7.5%Mn?1.5%Al?0.2%C steel after annealing at 650 ℃ and 665 ℃ (a), the volume fraction of austenite before and after tensile deformation (b), and the volume fraction of austenite transformed before and after swept by Lüders band (c)[22]
圖 4 Fe?0.2%C?10.2%Mn?2.8%Al?1%Si鋼冷軋板退火后顯微組織的電子背散射衍射（EBSD）相分布圖（a），拉伸應力?應變曲線（b），沿拉伸方向呂德斯帶的形核和傳播（c），三點彎曲ECCI原位表征奧氏體/鐵素體相界面上的位錯增殖過程（d），以及其相應的示意圖（e）[25]
Figure 4. Electron backscattered scattering detection (EBSD) phase map for the microstructures of cold rolled sheet of Fe?0.2%C?10.2%Mn?2.8%Al?1%Si after annealing (a), stress?strain curves (b), nucleation and propagation of Lüders band (c), multiplication of dislocation on austenite/ferrite interfaces examined by In-situ three-point bending ECCI (d), and the corresponding sketch map (e)[25]
圖 6 Fe?0.05%C?12%Mn?3%Al鋼熱軋退火試樣拉伸變形時各相之間的應變配分和拉伸力學性能. （a） 未變形試樣顯微組織的電子背散射衍射（EBSD）相分布圖；（b~e） 拉伸變形至1.8%，4.3%，8.4%，14%真應變時各相之間的范式等效應變分布圖；（f）工程應力?應變曲線；（g） 拉伸變形過程中回火馬氏體和殘余奧氏體或新鮮馬氏體之間的應變配分[29]
Figure 6. Strain partition and mechanical properties of the hot rolled Fe?0.05%C?12%Mn?3%Al steel after annealing: (a) the electron backscattered scattering detection (EBSD) phase distribution map for the microstructures before deformation; (b?e) von Miss strain distribution between different phases since tensile test interrupted at 1.8%, 4.3%, 8.4%, 14% true strain; (f) engineer stress?strain curve; (g) strain distribution between tempered martenstie, retained austenite or fresh martensite[29]
圖 8 Fe?0.14%C?7%Mn?0.23%Si鋼冷軋退火試樣的工程應力?應變曲線，呂德斯和PLC帶形核和傳播時應變和熱量的變化（a），以及拉伸變形時的奧氏體轉變量（b）[42]
Figure 8. Engineer stress?strain curves of the cooled rolled sheet after annealing for Fe?0.14%C?7%Mn?0.23%Si steel, the changing of strain and the heating during the nucleation and propagation of Lüders and PLC bands (a), and the amount of austenite transformed during tensile deformation (b)[42]
圖 9 Fe–C–Mn和Fe–C–Mn–N鋼的工程應力?應變曲線（a），（a）中藍色矩形區域的放大圖（b），Fe–C–Mn鋼（c）和Fe–C–Mn–N鋼（d）的應力鋸齒類型和PLC帶的形核位置[45]
Figure 9. Engineer stress?strain curves (a) of Fe–C–Mn and Fe–C–Mn–N steels, magnification view (b) of the area marked by blue rectangle in (a); the different types of stress serrations and the nucleation sites of PLC bands for Fe–C–Mn steels (c) and Fe–C–Mn–N steels (d)[45]
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