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Critical review on “Grain-‐boundary engineering markedly reduces susceptibility to intergranular hydrogen embrittlement in metallic materials.”
Guoqiang Xu
Department of Materials Science and Engineering, Massachusetts Institute of
Technology (MIT), Cambridge, MA 02139, USA S. Bechtle, M. Kumar, B. P. Somerday, M. E. Launey, R. O. Ritchie, Grain-‐boundary engineering markedly reduces susceptibility to intergranular hydrogen embrittlement in metallic materials. Acta Mater. 57, (2009) 4148-‐4157 [1] 1. Brief Summary
In this paper, S. Bechtle et. al. investigated the susceptibility of a nickel-‐based alloy to intergranular hydrogen embrittlement (HE). The nickel alloys are processed using cold rolling technique with different controlling parameters, resulting in different grain boundary (GB) microstructures. For the sample with high fraction of ‘special’ GBs, the tensile ductility in the presence of hydrogen is almost doubled compared to that in samples with low fraction of special GBs. Besides, the proportion of intergranular fracture was significantly lower for the former. The author attributes the reduction in the severity of H-‐induced intergranular embrittlement to the fact that the degree of hydrogen segregation at special GBs is lower. 2. Introduction
With increasing H content, the mechanical failure mode of metals changes, going from ductile transgranular, to ductile intergranular, to brittle intergranular [2]. Each of these transitions is associated with a marked reduction of overall fracture toughness [3]. The conditions at which these transitions occur and the degree of reduction in fracture toughness associated with them are functions of composition, loading configuration, and detailed microstructure, including the number and type of grain boundaries present in the material [4, 5]. GBs exhibit a variety of structures and properties, depending on their crystallography and atomic-‐level state. They may therefore be expected to exhibit differing susceptibilities to H-‐induced fracture. GB engineering can be used to change the number and type of GB in metallic alloys and therefore to manufacture alloys with better performance in H-‐rich environments [6, 7]. 3. Literature and concepts
Failure upon loading may occur through different fracture modes depending on the manner in which the crack propagates through a material. In ductile materials, crack propagation is accompanied by a large amount of plastic deformation [8], while in brittle materials cracks moves with little or no plastic deformation [9]. In polycrystalline materials, cracks propagation through the grains is called transgranular fracture. On the other hand, crack propagation along GBs is termed intergranular fracture. Fig. 1A illustrates intergranular and transgranular fracture.
Fig. 1 Schematic illustration of different fracture modes. (A) Intergranular and
transgranular fracture. (B) Cleavage and ductile fracture.
Ductile materials usually have high fracture toughness owing to the work of plastic deformation expended during crack advance. Fracture of most ductile materials proceeds by the nucleation, growth and coalescence of voids (Fig. 1B) [10]. Void nucleation usually takes place in regions of high local plastic deformation ahead of the crack tip, resulting in a fracture surface typically covered with hemispherical or hemi-‐ellipsoidal dimples [11]. Depending on the loading configuration and material properties, void coalescence may occur after a significant amount of void growth, which leads to a fracture surface covered with large and deep dimples, or start soon after the nucleation of voids, giving rise to shallow and small dimples [8, 12].
Some materials like diamond can undergo pure brittle fracture with no discernable plasticity associated with this process (Fig. 1B). Because no plastic work is expensed, the fracture toughness of such materials is therefore low. In addition to
pure brittle fracture where there is no plasticity, fracture can also be preceded by micro-‐plasticity, but void nucleation does not occur [13]. One example of this type of fracture is when dislocations emitted from a crack tip only shield the crack tip stress field and do not blunt a major portion of the crack front, allowing it to remain atomically sharp and to advance by atomic decohesion [9]. Another example is slip-‐induced cleavage, which occurs in the plastic zone ahead of and away from the crack tip [14].
Theoretically, ductile to brittle transition is attributed to the competition between two processes, decohesion and dislocation emission, as is shown in Fig. 2 [15-‐17]. If decohesion process is easier to happen, crack will propagate by slitting atom bonds in front of it and therefore the fracture mode is brittle. On the other hand, if dislocation emission is easier to happen, cracks will get blunted due to the dislocation nucleation with little extension. At the same time, the energy is dissipated through dislocation activities and the high stress fields at the crack tip are relieved, further preventing its propagation. At lower temperatures and/or high loads, dislocation activities also lead to void formation, resulting in crack propagation by void coalescence.
Fig. 2 The competition between decohesion and dislocation emission determines the
ductile to brittle transition behavior of metals.
Based on this criterion, H may influence ductile to brittle transition by influencing the decohesion process as well as dislocation emission process. H generally reduces the maximum cohesive force between two atomic layers and therefore makes it easier for decohesion. Carter calculated the ideal fracture energy of iron and aluminum in the presence of varying amounts of H using periodic density functional theory [18]. He found that the ideal fracture energy decreases almost linearly with increasing H coverage, dropping by ~45% at one-‐half monolayer coverage and indicating a substantial reduction of cohesion in the presence of H, as is shown in Fig. 3.
Fig. 3 Decrease in normalized surface energies !(!)/ !(0) for H covered
Al (111) and Fe (110) as hydrogen coverage ! increases. (Figure copied from Fig. 3 of Ref. [18])
Oriani also proposed Hydrogen Induced Decohesion as a mechanism for HE
[19-‐22] and supported this experimentally by tensile loading of pre-‐cracked AISI 4340 steel in a H atmosphere [22]. These experiments showed that as the partial pressure of H increases, the critical stress intensity at the crack tip needed to restart crack propagation decreases, indicating that H decreases the maximum cohesive force between atomic layers and embrittles these crystals, as is shown in Fig. 4.
Fig. 4 Pressures of hydrogen and deuterium, marked by a short dash, at which the crack remained stationary prior to the pressures at which the crack propagated,
marked by a circle for H, and a square for D, at various stress-‐intensity factors, K. (Figure copied from Fig. 2 of Ref. [22])
On the other hand, hydrogen may influence the dislocation process through
its interaction with dislocations. By considering the size misfit strain energy, Rice calculated the energy release rate for the emission of a straight-‐line dislocation in the presence of H [23]. Theoretical analysis showed that the role of H is to pin the movement of dislocations, making dislocation emission harder. This pinning effect favors brittle fracture. In addition to the size effect, hydrogen may also interact with dislocations by increasing dislocation mobility and allows highly localized deformation [24, 25]. This is the Hydrogen-‐Enhanced Local Plasticity proposed by Beachem as a mechanism for HE. The HELP model suggested that the enhanced plasticity would result in localized softening, which leads to failure by plastic flow localization, in contrast to the usual sense of embrittlement. Some in situ environmental cell transmission electron microscopy (TEM) measurements have been interpreted as lending support to this mechanism [26].
Different GBs have different susceptibilities to intergranular HE. For example, Wang worked out the degree of susceptibility of GBs to bismuth embrittlement, as shown in Fig. 5. The results clearly indicated that Σ11 GB is more susceptible to bismuth embrittlement than Σ 9 and Σ41 [27]. All the factors that influence the energy release rates for cleavage and dislocation emission may play a role in determining GB susceptibility to HE. Those include the binding energy of H at the trapping sites of the GBs, the reduction of ideal interface separation energies at certain H concentration, as well as the shielding of GB stress field in the presence of H.
Fig. 5 Predictions of the Rice-‐Thomson model for cleavage response versus
dislocation emission at interfacial cracks. (Figure copied from Fig. 13 of Ref. [27])
4. Discussion on the results
The author shows that GB engineering can be used to control the microstructures. For samples of the same size, two different thermomechnaical processes are adopted. For one sample, three cycles of cold rolling (5% reduction in the thickness per cycle) followed by a 15 min anneal at 900 degrees in air furnace (water quenched), resulting a microstructure with a high length fraction of 75% special boundaries (62% number fraction). For the other sample, four cycles of cold rolling (20% reduction in thickness per cycle) followed by a 15 min anneal at 700 degrees in an air furnace (water quenched) with a final 1 hour grain-‐coarsening anneal at 900 degrees, resulting in a low length fraction of 46% special boundaries (35% number fraction). Moreover, all the special GBs in the second sample are !3 twin boundaries. Fig. 6, taken from this paper, shows the EBSD orientation mapping of the microstructures, with !3! special boundaries in blue and !3 twin boundaries in red.
Fig. 6. EBSD orientation maps of the grain structures in Ni-‐201 of the
microstructures with a (A) low fraction (46% by length) and (B) high fraction (75% by length) of special grain boundaries. Random boundaries are depicted in black, R3 twin boundaries in red, and other R3n special boundaries in blue. Grain size and texture remain essentially unchanged. (Figure copied from Fig. 1 of the paper)
The interesting question arisen from this result is that what is the
mechanism for using GB engineering to change the microstructures. One proposed mechanism is called the ‘!3 regeneration mechanism’ [28]. The central point of the mechanism is that when two !3s boundaries meet, a !9 boundary is formed to
complete the triple junction. When such a !9 boundary encounters another !3, a new !3 boundary (importantly, not a coherent annealing twin) will be regenerated according to !3! + !3!!! → !3.
This process has three requirements. First, a threshold level of !3s in
materials before the thermomechnaical processing is required. This is because if the fraction of !3 GBs is too small, chances are small for two !3s to meet each other and react. This also indicates that profuse annealing twinning is a prerequisite for most GB engineering. Secondly, the thermomechnaical process has to be iterative. Otherwise, the regeneration described above could only occur once and therefore it is not able for the sample to be abundant in !3! special boundaries. Last, there has to be a driving force for selective grain boundary migration such that special boundaries, mainly incoherent !3s and some !9s will migrate preferentially. This is why annealing must be followed after each cold rolling.
In nanocrystalline materials, the volume fraction of GB (50% for 5 nm grains,
30% for 10 nm grains) reaches very high value and therefore the interface structure can dictate the macro mechanical properties [29]. However, the average grain size in both samples in this work is around 30 !", indicating that the volume fraction of GBs is extremely small. It is interesting why GBs could play such an important role here. One of the reasons may be that H prefers to segregate to the GBs and cause intergranular fracture. Crack propagation paths are within the connected GB networks, which makes GB type and structure important in improving the fracture property of materials.
Another important finding in this work is that in the presence of H
concentrations between 1200 and 3400 appm, the high special fraction microstructure showed almost double the tensile ductility; also, the proportion of intergranular fracture was significantly lower. It’s still not clear how those special GBs can influence the susceptibility of HE in alloys. According to the literature, the role of H in the fracture process is quite complicated. Not only can it reduce the maximum cohesive force along the interface, hence facilitating decohesion process, but it can also shield the interactions between dislocations, increase the mobility of dislocations, finally leading to the highly localized deformation bands.
Fig. 7 Binding energy of H at different GBs, computed from atomistic simulations.
(Figure from Ref. [30])
The author attribute the reduction in the severity of H-‐induced intergranular embrittlement to the fact that the binding energy of H at special !3! GBs is small and therefore, less H is segregated at there boundaries. However, literature shows that the binding energy of H at !3! is not differ much from that of other GBs. Baskes showed using atomistic simulations that Σ3 (112) and Σ11 (113) GBs in nickel have a maximum trapping energy of 0.24eV while at Σ9 (221) GBs it is 0.28eV [30]. Hickel studied interaction of H interstitials with GBs in alpha-‐iron and gamma-‐iron by density functional theory and showed that the trapping energies for H at Σ3 (112) and Σ11 (113) GBs are 0.18eV while that for Σ5 (310) GB is much lower and only 0.05eV [31]. Ferthermore, even at the same H coverage, the reduction of ideal interface separation energy for different GBs in the presence of H may be different. Hickel showed that for Σ3 GBs in alpha iron, the interface separation energy reduced by 33.1% while for Σ5 GBs it only decreased by 11.2% [31].
References
1. S. Bechtle, M. Kumar, B. P. Somerday, M.E. Launery and R.O. Ritchie, Acta Materialia 57 (2009) 4148-‐4157.
2. R. H. Jones, S. M. Bruemmer, M. T. Thomas and D. R. Baer, Metall. Trans. A 14 (1983) 1729.
3. Petr Hausild, Ivan Nedbal, Clotilde Berdin and Claude Prioul, Materials Science and Engineering A 335 (2002) 164-‐174.
4. N. Ben Ali, D. Tanguy and R. Estevez, Scripta Materialia 65 (2011) 210-‐213. 5. Yuan Yao, Xiaolu Pang and Kewei Gao, International Journal of Hydrogen
Energy 36 (2011) 5729-‐5738. 6. V. Randle, Acta Mater. 52 (2004) 4067. 7. M. Kumar and C.A. Schuh, Scr. Mater. 54 (2006) 961. 8. T. Pardoen and Y. Brechet, Philosophical Magazine 84 (2004) 269-‐297. 9. Z. Suo, C.F. Shih and A.G. Varias, Acta Metall. Mater. 41 (1993) 1551-‐1557. 10. V.A. Lubarda, M.S. Schneider, D.H. Kalantar, B.A. Remington and M.A. Meyer,
Acta Materialia 52 (2004) 1397-‐1408. 11. T. Pardoen, I. Doghri and F. Delannay, Acta Mater. 46 (1998) 541-‐552. 12. Imad Barsoum and Jonas Faleskog, International Journal of Solids and
Structures 44 (2007) 1768-‐1786. 13. T.C. Wang, Philosophical Magazine A, 74 (1996) 983-‐1001. 14. Kwai S. Chan and David L. Davidson, Metallurgical and Materials Transactions
A 30 (1999) 925. 15. James R. Rice and Robb Thomson, Phil. Mag. 29 (1974) 73. 16. James R. Rice, J. Mech. Phys. Solids 40 (1992) 239-‐271. 17. James R. Rice and Glenn E. Beltz, J. Mech. Phys. Solids 42 (1994) 333-‐360. 18. D.E. Jiang and E.A. Carter, Acta Materialia 52 (20040 4801-‐4807. 19. R.A. Oriani, Acta Metallurgica 18 (1970) 147. 20. R.A. Oriani and P.H. Josephic, Acta Metallurgica 25 (1977) 979-‐988. 21. R.A. Oriani and P.H. Josephic, Scripta Metallurgica 6 (1972) 681-‐688. 22. R.A. Oriani and P.H. Josephic, Acta Metallurgica 22 (1974) 1065. 23. J. Yu and J. R. Rice, Interfacial Structure, Properties and Design 122 (1988)
361.
24. M. Dadfarnia, P. Novak, D.C. Ahn, J.B. Liu, P. Sofronis, D.D. Johnson and I.M. Robertson, Advanced Materials 22 (2010) 1128-‐1135.
25. H.K. Birnbaum and P. Sofronis, Materials Science and Engineering A 176 (1994) 191-‐202.
26. Y. Murakami, T. Kanezaki and Y. Mine, Metallurgical and Materials Transactions A 41A (2010) 2548.
27. Jian Sheng Wang and P.M. Anderson, Acta Metall. Mater. 39 (1991) 779-‐792. 28. V. Randle, Acta Mater. 47, (1999) 4187. 29. Y. H. Zhao, T. T. Zhu, E. J. Lavernia, Adv. Eng. Mater. 12, (2010) 769. 30. J.E. Angelo, N.R. Moody and M.I Baskes, Modelling Simul. Mater. Sci. Eng. 3
(1995) 289-‐307. 31. Yaojun A. Du, L. Ismer, J. Rogal, T. Hickel, J. Neugebauer and R. Drautz,
Physical Review B 84 (2011) 144121.