Advances in Materials Science and Engineering

Advances in Materials Science and Engineering / 2018 / Article

Research Article | Open Access

Volume 2018 |Article ID 1713835 |

Xiangjun Xu, Rui Hu, Junpin Lin, Jian Guo, "Evolution of Microstructure and Microsegregation of Ti-45Al-8Nb Alloy during Directional Solidification", Advances in Materials Science and Engineering, vol. 2018, Article ID 1713835, 9 pages, 2018.

Evolution of Microstructure and Microsegregation of Ti-45Al-8Nb Alloy during Directional Solidification

Academic Editor: David Holec
Received04 Jul 2018
Accepted02 Sep 2018
Published08 Oct 2018


High Nb-containing TiAl alloys have good oxidation resistance and mechanical properties, but the microstructure and the properties are substantially affected by the segregation. To quantitatively investigate the segregation behavior of Al during solidification, microstructures of directionally solidified (DS) Ti-45Al-8Nb (in atomic percent) alloy prepared at withdrawing rates of 30 μm/s and 200 μm/s and a temperature gradient of 4200 K/m were observed by optical microscope and electronic probe microanalyzer. The microsegregations were characterized by wave dispersive spectroscopy. The results show that the DS ingots include the no melting zone, directionally solidified zone with columnar grains, mushy zone, and quenched liquid zone. The primary dendritic arm spacings are 353 μm and 144 μm, respectively, for the two ingots. But the solidified microstructures of the ingots are large lamellar colonies, which contain a few B2 patches and γ bands induced by microsegregation. From dendritic zone to columnar zone, the volume fractions of B2 patches and γ bands decrease. The segregation extents of Al and Nb decrease with the increase of solidification rate. There exists an obvious back diffusion process of Al during solidification and cooling after solidification. According to evolution of Al concentration profiles from mushy zone to columnar grain zone, interdiffusion coefficient for Al in β-Ti at near solidus temperature is semiquantitatively calculated, and the value is (6 – 11) × 10−11 m2/s.

1. Introduction

High Nb-containing TiAl alloys have garnered increasing attention due to their excellent properties, which are superior to those of conventional TiAl alloys, especially at high temperatures [16]. For example, the yield strength of Ti-45Al-8Nb alloy with fully lamellar structure is 505 MPa at 900°C because Nb increases Peierls stress of lattice and the interaction between dislocations and improves the high temperature stability of microstructure of the TiAl alloys [1]. The oxidation behavior of TiAl alloy is significantly improved by Nb addition. Pentavalent niobium ion could substitute for tetravalent titanium ion in TiO2 oxide. The (Ti, Nb)O2-rich layer is dense and chemically uniform, which is more protective than the TiO2 layer [6]. So this kind of TiAl alloys has been developed over the past twenty years and is beginning to use in both automotive and aerospace industries [7, 8]. However, microsegregation of Al and Nb elements can be easily induced in the castings of the alloys. It is known that the microstructure and the mechanical properties are very sensitive to the Al content for TiAl alloys [9], and the volume fraction of B2 and ω phases is sensitive to Nb content for high Nb-containing TiAl alloys [10, 11]. Thus, reducing and eliminating the microsegregation in casting are necessary for obtaining optimal properties for high Nb-containing alloys. A thorough understanding of evolution of microstructure and microsegregation during solidification should be of great importance for prediction of material properties and for design of postcasting heat treatment processes. Microstructures of Ti-Al-Nb ternary alloys have been studied by many groups. For example, Shuleshova et al. have in situ observed the primary phase of 15 Ti-Al-Nb alloys by synchrotron radiation [12]; Ding et al. have analyzed L + β ⟶ α peritectic reaction of Ti-46Al-5Nb and Ti-45Al-6Nb-0.3B alloys and prepared single lamellar grain with lamellar boundaries parallel to the ingot growth direction by double directional solidification [13]; Oering et al. and Klein et al. have studied β ⟶ α transformation of Ti-45Al-(5–7)Nb-(0.5–1)Mo-(0–0.2)B alloys and TNM alloy, respectively [14, 15]. However, there is scarce work quantitatively reported on the microsegregation behavior of high Nb-containing TiAl alloys as yet, especially on the element distribution and microsegregation evolution during solidification and cooling processes [16, 17]. The present work will investigate the microstructures and compositions of directionally solidified (DS) Ti-45Al-8Nb (in atomic percent) alloy in order to clarify the microsegregation evolution behavior and its effect on the microstructure during solidification and cooling procedures.

2. Experimental

The 1 kg button ingot with nominal composition of Ti-45Al-8Nb was prepared by nonconsumable arc melting (tungsten electrode) of the high purity elements, that is, Ti (99.99 wt.%), Al (99.99 wt.%), and Nb (99.99 wt.%), using a water-cooled copper hearth in a gettered ultra-high-purity argon atmosphere. With the inert gas fusion infrared method, we tested the oxygen content of the ingot, and the value was 360 ppm. The rods with each dimension of Φ6.8 × 100 mm were cut from the button ingot using electric spark machining for DS processes. The rod was inserted in a Φ8 × 126 mm dense cylindrical alumina crucible covered with a 0.3 mm thick layer of yttria to keep alloy from reacting with the crucible and mounted in a modified Bridgman-type apparatus (Figure 1). Two DS processes are performed at a thermal gradient of 4.2 K/mm and withdrawing rates of 30 μm/s and 200 μm/s, respectively. After withdrawing 50 mm, the ingots were quenched to capture the morphologies of the dendrites.

The solidified ingots were firstly cut longitudinally. Half of each ingot was metallographically polished and etched to observe macrostructure using an OLYMPUS-BX51M optical microscope. Two transverse sections in each ingot, corresponding to the mushy zone and fully solidified zone, respectively, which are 5 mm apart, were positioned from the observed half and cut from another half of the ingot. The four transverse sections were mounted into bakelite puck and metallographically polished. Then, they were analyzed with a JEOL JXA-8230 electron microprobe (EPMA) equipped with four wavelength dispersive spectrometers (WDS) and one back-scattered electron (BSE) detector. An area-scan method was adopted to determine the microsegregation behavior of each transverse section. 121 points within an area of 400 × 400 μm on each section, which encompassed more than one primary dendrite arm, were measured the compositions automatically. After collecting the data, regardless of their sampling locations, Al series is arranged into ascending order and Nb series is arranged into descending order obeying rank number from 1 to 121. Then, each Al (applied equally to Nb) is assigned to a fraction solid. A fraction solid fs at rank number, Ri, is the ratio of Ri to the total number of sampled points, 121. Finally, continuous composition profiles for Al and Nb elements were produced. The principle of constructing composition profiles is expounded in Reference [18]. Some sections were observed on a Tecnai G2 F30 transmission electron microscope (TEM) to reveal microstructural details. Foil samples for the TEM experiment were mechanically ground to 50 µm and subsequently thinned by twin-jet polishing in an electrolyte containing 30 ml perchloric acid, 175 ml butyl alcohol, and 300 ml methanol at 30 V and −30°C.

3. Results and Discussion

3.1. Macrostructures of the DS Ingots

Each DS ingot includes 4 zones, which we designate the no melting zone, columnar DS zone, mushy zone, and quenched zone. The no melting zone with original nearly lamellar (NL) microstructure is the bottom part of the ingot, which is on the top of the withdrawing rig. Because the withdrawing rig is in Ga-In-Sn liquid metal within water-cooled copper die, the bottom part of the rod is nearly at room temperature and cannot be melted during heating. With the increase of the distance from the bottom of the rod, the rod was heated to α phase region and the grains grew up, forming a coarse-sized fully lamellar (FL) microstructure after cooling to room temperature. Upon this zone, the rod melts in the crucible. By withdrawing the crucible and the rod, the melt was cooled and DS ingot formed. Figure 2 is part of macrostructure of the longitudinal section of the 30 μm/s withdrawn DS ingot. The left of the image is oriented to the bottom of the ingot and the heat extraction direction. It is a columnar structure with the preferential growth direction nearly parallel to axis of the ingot, showing coarsening of the primary dendrite arms and disappearance of the secondary dendrite arms for holding at high temperature after solidification. Above the columnar grain, the mushy zone appears typical dendrite microstructure, coexisting with the quenched microstructure in the interdendritic zone. The 200 μm/s withdrawing DS sample has the similar macrostructure. The distinct difference of the two ingots is the primary arm spacing, which is 353 μm for the 30 μm/s withdrawn DS ingot and 144 μm for the 200 μm/s withdrawn DS ingot.

3.2. Microstructure Evolution

Figure 3 is the microstructures of the mushy zone of the 30 μm/s withdrawing DS ingot obtained by observing the transverse section (named section 30-1 hereafter). Secondary dendrite arms are oriented at an angle of 90° to each other. Besides well-developed secondary arms, tertiary dendrite arms orientated at an angle of 90° to the secondary arms can also be clearly identified (Figure 3(a)). According to the 8Nb containing Ti-Al quasi-phase diagram and the fourfold symmetry of dendrites, it is concluded that primary solidification phase is β phase. This is in accordance with the results of Shuleshova, which were drawn after in situ observation by synchrotron radiation and showed that the alloys with 43.5–46.4Al and about 8Nb completely solidified with single β as the primary phase [12]. Higher-magnification BSE images of transverse section in mushy zone show that the composition of a dendrite does not transit from the spine to the edge, but Nb-rich (white contrast) networks with a width of 1–4 μm distribute in grey contrast matrix (Figure 3(b)). TEM analysis indicates that the grey matrix in Figure 3(a) is γ//α2 lamellar colonies, whereas the network is B2 phase (Figure 3(c)). It is clear that even quenching procedure cannot restrain β ⟶ α + β and α ⟶ γ + α2 transformations, and Nb element undergoes distinguishable redistribution through β ⟶ α + β transformation. During β ⟶ α + β transformation, the Al diffuses into α phase, while the β stabilization element Nb diffuses to opposite direction. This tendency leads to enrichment of Nb and depletion of Al at the interfaces between β and α phases. Finally, the untransformed β area or the boundaries between transformed α grains abound in Nb. These zones evolve into B2 phase during quenching at higher cooling rate [19]. This is also identified by TEM selected area electron diffraction (SAD) pattern of these zones (Figure 3(d)).

Figure 4 shows the microstructure of columnar zone of the 30 μm/s withdrawing DS ingot by observing a transverse section 5 mm below that shown in Figure 3 (named section 30-2 hereafter). Though the secondary arms and the tertiary arms disappear, the primary arms are delineated by the Al-rich lines with dark contrast. Also the white vermiform bands rich in Nb are obvious. Compared with Figure 3(a), the density of the white bands is sparse and the width of the bands is thick (Figure 4(a)). Higher-magnification image shows most of the white bands and the black lines are lamellar structures (Figure 4(b)). Very few patches in the white bands are B2 and limited black lines are γ phase. The columnar zone also undergoes β ⟶ α + β transformation, and this process is a near-equilibrium process at the present growth rate. Thus, α grains have enough time to grow up and engulf many original Nb-rich α grain boundaries or Al-rich dendrite boundaries, leading to coarse-sized lamellar colony containing vermiform bands with different contrasts. Also it has enough time for elements to diffuse and redistribute, leading to a less extent of microsegregation. This will be characterized semiquantitatively in Section 3.3.

Figure 5 shows the BSE images of transverse sections corresponding to the mushy zone and the columnar zone of the 200 μm/s withdrawn ingot (named section 200-1 and section 200-2, respectively, hereafter). The morphology of the mushy zone is similar to that of section 30-1, except for the two aspects: (1) the dendrites are more typical and clear dendritic arms are observed, and (2) the primary and secondary arm spacings are decreased (Figure 5(a)). The primary arm spacing is 144 μm. These are normal phenomena, because the microstructure of the mushy zone exhibits a cellular-dendritic structure at lower growth rate and a typical dendritic morphology at higher growth rate [20] and dependence of primary dendritic arm spacing on growth rate obeys kv−1/4 relationship, where k is a constant and is the solidification rate [21]. Analogously, dependence of secondary dendritic arm spacing on growth rate obeys Mv−1/3 relationship, where M is a constant and is the solidification rate [22]. Fine dendritic arm spacing for the ingot with higher growth rate is beneficial for eliminating the microsegregation by heat treatments because the annealing time required to homogenize is proportional to the square of dendritic arm spacing [23]. High-magnification image also shows that Al-rich bands with black contrast are γ phase and Nb-rich nets with bright contrast are B2 phase. Low-magnification BSE images of section 200-2 show that outline of primary dendrite disappears. The trace of Al in interdendritic zone is hardly discerned. The Nb-rich zones show white needle morphology with several millimeters long or a network morphology with the mesh of about 100 μm. Why Nb distributes in such forms is not clear. High-magnification images show that section 200-2 is also fully lamellar structure with few B2 phase. The α grains in section 200-2 are lathy morphology (Figures 5(c) and 5(d)), quite different from the equiaxed morphology in section 30-2 (Figure 4). So, at higher cooling rate, α plates precipitating from β grain boundaries form a Widmannstätten-type structure. This structure is also found by Oering et al. in Ti-45Al-(5–7)Nb-(0.5–1)Mo-(0–0.2)B alloys [14]. Klein et al. quantitatively studied this phenomenon in TNM alloy and pointed out that low cooling rates rendered equiaxed α grains, whereas high cooling rates led to the formation of lath-like (Widmannstätten) structures [15]. At various cooling rates, growth up and annexation of α grains are so conspicuous that fully lamellar colonies with large size form.

3.3. Microsegregation Evolution

Figure 6 shows the measured concentration profiles of Al and Nb in section 30-1 and section 200-1, representing the mushy zone, and in section 30-2 and section 200-2, representing the columnar grains zone. For comparing and easily identifying microsegregation behavior, the concentration profiles are arranged in different ways. Figure 6(a) is the Al concentration profiles in section 30-1 and section 200-1. It is obviously seen that the segregation extent is severer in section 30-1 than in section 200-1, and microsegregation ratios of Al (the ratio of the maximum Al content to the minimum Al content) for the two mushy zones are 1.19 and 1.15, respectively. The differences of the maximum and the minimum Al contents in section 30-1 and section 200-1 are 8.48 at.% and 6.49 at.%, respectively. The concentration profiles of Nb are shown in Figure 6(b). For the differences of the maximum and minimum Nb contents, the trend of decrease with the increase of the solidification rate is not found. This is maybe because B2 and γ phases affect the test results of Nb content. Even so, it is concluded that the distribution of alloy elements in dendritic structure formed at high solidification rate is more uniform than that in dendritic structure formed at low withdrawing rate. This results from the difference of the dendritic arm spacing. The dendrite has a finer arm spacing that induced three effects: (1) the solute is hard to accumulate between finer spacing arms for the larger solid/liquid interface; (2) easy impinging of solute fields in the solidification fronts of two arms increases the concentration gradient in liquid; and (3) the permeability of the interdendritic channels is low, convective mass flow in the liquid is hindered, and boundary layer is constructed before the solid/liquid interface [24]. These factors are beneficial for strong accumulation of Al in the liquid at the solid/liquid interface, thus leading to Al back-diffusion in solid and increase of Al content in the solid and uniform element distribution within longer fraction solid.

Figure 6(c) shows the Al concentration profiles in section 30-2 and section 200-2. As in Figure 6(a), segregation extent is severer in section 30-2 than in section 200-2, and the microsegregation ratios of Al for these two sections are 1.10 and 1.04, respectively. The differences of the maximum and the minimum Al contents in section 30-2 and section 200-2 are 4.26 at.% and 1.83 at.%, respectively. This trend is also shown in Figure 5(d), the Nb concentration profiles in these two sections. The distinguishable Nb segregation in these two sections is attributed to the scarce of B2 and γ blocks, whose compositions cannot be acquired by WDS to cover up the truth. Segregation ratios of Nb (ratio of the maximum Nb content to the minimum Nb content) in section 30-2 and section 200-2 are 1.45 and 1.27. By comparing the Al or Nb concentration profiles from the two sections of the same ingot, it is worthy to note that segregation extent obviously decreases during solidification and microstructure evolution. The segregation ratios of Al decrease from 1.19 of mushy zone to 1.10 of columnar zone in the 30 μm/s withdrawn ingot (Figure 6(e)) and from 1.15 of mushy zone to 1.04 of columnar zone in the 200 μm/s withdrawn ingot (Figure 6(f)).

Figures 6(e) and 6(f) also show the calculated concentration profiles of Al, which is based on the thermodynamic database of Witusiewicz using Pandat software [25]. At present, the calculation can only be made for the Scheil model, which is based on the assumptions of complete mixing in the liquid but no diffusion in the solid. The concentration profiles of Al in the two sections of each ingot deviate from the calculated result, that is, actual Al distribution is more uniform than the Al distribution predicted by the Scheil equation. This indicates that the back diffusion of Al upon solidification cannot be ignored. The above continuous composition profiles are produced by assuming that the solid concentration varies continuously with fraction solid. However, the element partition associated with β ⟶ α + β transformation is opposite to the element partition during solidification. Though the redistribution can be seen, this is hard to be tackled and neglected in the construction of concentration profiles. Even so, it is concluded that back diffusion of Al is an incessant and considerable process during solidification of high Nb-containing TiAl alloys. So, if we analyze and calculate the element distribution during solidification, using Scheil mode or ignoring back diffusion of Al is not reasonable. The smaller the primary arm spacing, the more prominent the back diffusion of Al.

3.4. Interdiffusion Coefficient for Al in β-Ti at near Solidus Temperature

Comparing the microsegregation extent of Al or Nb in mushy zones (section 30-1 and section 200-1) and that in columnar zones (section 30-2 and section 200-2), one can say that solidified ingots are subjected to a homogenization heat treatment during the withdrawing processes. The evolution of Al concentration profiles from mushy zone to columnar grain zone can be thought as a result of homogenization of Al interdendritic segregation for diffusion in β-Ti. The interdiffusion coefficient for Al in β-Ti () at near solidus temperature can be semiquantitatively calculated from the concentration profiles.

In order to determine the homogenization of the β-Ti occurred during its solidification and cooling, only one dendrite arm needs to be considered for the periodical element distribution (the cycle is primary arm spacing λ). The Al concentration profiles in section 30-2 and section 200-2 evolved from those in section 30-1 and section 200-1 after 167 s and 25 s, respectively. The times are obtained by the quotients of the distance of the two sections (5 mm) and drawing rates (30 μm/s and 200 μm/s, respectively). The change is approximately treated by using the one-dimensional time-dependent diffusion equation:where is the evolution time, is the vertical distance from the boundary of the considered dendrite arm and its neighbor to the calculated location, and is the concentration of Al at location and time . What is the effect of Nb on the diffusion behavior of Al in β-Ti at high temperature is not clear. It is speculated that the effect of Nb is not considerable because Nb and Ti have the similar atomic size (atom radius of Nb is 1.46 Å and atom radius of Ti is 1.47 Å) and Nb diffuses in titanium with the diffusion coefficient very near that for self-diffusion of Ti at high temperatures [26]. So, we consider Al as the solute and Ti + Nb as the solvent of the alloy, and the process is simplified down to a binary diffusion phenomenon.

The concentration distributions of Al in the primary dendrites do not happen to be sinusoidal. However, because the diffusion equation is linear, any number of similar equations can be added together, and according to Fourier analysis, any solute distribution can be described by a sum of a sine or cosine series and a constant. For the present problem, the simple sinusoidal concentration variation is quite useful because the higher-order terms decay much more rapidly than the longer ones, and the homogenization process will be ultimately determined by the relaxation time of the lowest-order term [23]. So the initial concentration variation of Al is approximately given bywhere is the average concentration of Al, is the initial amplitude of the concentration variation at boundary of dendrite arms, and λ is the primary dendritic arm spacing. The maximum concentration for the lowest-order term at x = 0, , changes with time according to the following equation:where . Substitution of the corresponding experimental values (Table 1) into Equation (3) yields and for the 30 μm/s withdrawn ingot and and for the 200 μm/s withdrawn ingot. The increase of the value of with the increase of solidification rate is because the contribution of the secondary dendrite to diffusion is ignored. The calculated is proportional to . If the contribution of the secondary dendrite to diffusion is considered, the average diffusion distance of Al decreases more significantly for higher rate withdrawn ingot because it has well-developed and finer secondary dendrite. Thus, the values of decrease correspondingly, and there should be a greater decrease for the 200 μm/s withdrawn ingot compared with the 30 μm/s withdrawn ingot. Maybe a complex correction for the calculation method results in two calculated values of quite according to each other.

(at.%)Cm (at.%)λ (m)T (s) (s) (m2/s)

44.8845.813.53144 × 10−62518.7

The abovementioned diffusion behavior of Al takes place at the temperature near the solidus temperature of the alloy and within a temperature range of 21°C, which can be obtained by the product of distance of the two sections (5 mm) in the same ingot and the temperature gradient (4.2°C/mm). Based on the thermodynamic database of Witusiewicz [25], we calculated the solidus temperature of Ti-45Al-8Nb alloy by Pandat software and obtained the value of 1530°C. So we can say interdiffusion coefficient for Al in β-Ti is about  m2/s at about 1530°C. It is 4–11 times higher than the results of Sung-Yul Lee determined by Matano's method for lower Al content β-Ti (about  m2/s for Ti-(Ti-8.5 at.% Al) couple) [27]. Apart from simplified calculation method, this is partly attributed to the higher Al content of the present alloy, for the value of increases gradually with increasing aluminum content [27]. Although the values are semiquantitative results for neglecting Nb addition and considering solidification and cooling together, they have practical significance in designing heat treatment process to eliminate Al microsegregation for high Nb-containing TiAl alloys.

4. Conclusions

Ti-45Al-8Nb alloy directionally solidified at temperature gradient of 4.2 K/mm and withdrawing rate of 30 μm/s and 200 μm/s, and the microstructures and the compositions of ingots were analyzed. The following conclusions can be drawn.(1)Macrostructures show that both ingots are composed of columnar zone and dendritic zone, and the primary dendrite arm spacings are 353 μm for the 30 μm/s withdrawn ingot and 144 μm for the 200 μm/s withdrawn ingot, respectively. But the microstructures of the ingots are lamellar colonies, containing a few B2 patches and γ bands. The γ bands result from Al segregation during L ⟶ β solidification and the B2 patches result from Nb segregation during α ⟶ α + β transformation. From dendritic zone to columnar zone, the B2 patches and γ bands decrease.(2)The segregation extents of Al and Nb decrease with the increase of solidification rate for the finer dendrite arm spacing is beneficial for diffusion of elements, and Al back diffusion during solidification and the diffusion during cooling after solidification is obvious. So, solidified ingots experience a homogenization process during their preparation.(3)After simplifying down to a binary diffusion mode, a semiquantitatively calculated Al interdiffusion coefficient in β-Ti is m2/s at near solidus temperature.

Data Availability

The measured data used to support the findings of this study are included within the supplementary information file.

Conflicts of Interest

The authors declare that there are no conflicts of interest regarding the publication of this paper.


This research was supported by the fund of the State Key Laboratory of Solidification Processing in NWPU (no. SKLSP201647), the National Natural Science Foundation of China (no. 51671016), and Henan Natural Science Foundation (no. 162300410342). The work was also supported by Chongqing Science and Technology Commission under the contract of cstc2018jcyjAX0727.

Supplementary Materials

The data are the original data used to plot Figure 6. Column 2 is the fraction solid, columns 3 through 6 are the Al contents for the four sections, and columns 7 through 10 are the Nb contents for the four sections, respectively. (Supplementary Materials)


  1. Z. C. Liu, J. P. Lin, S. J. Li, and G. L. Chen, “Effects of Nb and Al on the microstructures and mechanical properties of high Nb containing TiAl base alloys,” Intermetallics, vol. 10, no. 7, pp. 653–659, 2002. View at: Publisher Site | Google Scholar
  2. J. P. Lin, X. J. Xu, Y. L. Wang et al., “High temperature deformation behaviors of a high Nb containing TiAl alloy,” Intermetallics, vol. 15, no. 5-6, pp. 668–674, 2007. View at: Publisher Site | Google Scholar
  3. J. Li, Y. Liu, B. Liu, Y. Wang, X. Liang, and Y. He, “Microstructure characterization and mechanical behaviors of a hot forged high Nb containing PM-TiAl alloy,” Materials Characterization, vol. 95, pp. 148–156, 2014. View at: Publisher Site | Google Scholar
  4. M. Kastenuber, B. Rashkova, H. Clemens, and S. Mayer, “Enhancement of the application temperature of titanium aluminides,” BHM, vol. 160, no. 7, pp. 342–345, 2015. View at: Publisher Site | Google Scholar
  5. G. Chen, Y. Peng, G. Zheng et al., “Polysynthetic twinned TiAl single crystals for high-temperature applications,” Nature Materials, vol. 15, no. 8, pp. 876–881, 2016. View at: Publisher Site | Google Scholar
  6. J. P. Lin, L. L. Zhao, G. Y. Li et al., “Effect of Nb on oxidation behavior of high Nb containing TiAl alloys,” Intermetallics, vol. 19, no. 2, pp. 131–136, 2011. View at: Publisher Site | Google Scholar
  7. B. P. Bewlay, S. Nag, A. Suzuki, and M. J. Weimer, “TiAl alloys in commercial aircraft engines,” Materials at High Temperatures, vol. 33, no. 4-5, pp. 549–559, 2016. View at: Publisher Site | Google Scholar
  8. Y. W. Kim and S. L. Kim, “Advances in gammalloy materials–processes–application technology: successes, dilemmas, and future,” JOM, vol. 70, no. 4, pp. 553–560, 2018. View at: Publisher Site | Google Scholar
  9. X. J. Xu, J. P. Lin, and D. D. Han, “Effect of Al on microstructures and properties of Ti-45Al-8.5Nb-0.2B-0.2W alloy,” Materials Science Forum, vol. 747-748, pp. 44–49, 2013. View at: Publisher Site | Google Scholar
  10. L. Song, L. Q. Zhang, X. J. Xu, J. Sun, and J. P. Lin, “Omega phase in as-cast high-Nb-containing TiAl alloy,” Scripta Materialia, vol. 68, no. 12, pp. 929–932, 2013. View at: Publisher Site | Google Scholar
  11. Z. W. Huang, W. Voice, and P. Bowen, “Thermal exposure induced α2+γ⟶B2(ω) and α2⟶B2(ω) phase transformations in a high Nb fully lamellar TiAl alloy,” Scripta Materialia, vol. 48, no. 1, pp. 79–84, 2003. View at: Publisher Site | Google Scholar
  12. O. Shuleshova, D. Holland-Moritz, W. Löser et al., “In situ observations of solidification processes in γ-TiAl alloys by synchrotron radiation,” Acta Materialia, vol. 58, no. 7, pp. 2408–2418, 2010. View at: Publisher Site | Google Scholar
  13. X. F. Ding, J. P. Lin, L. Q. Zhang, Y. Q. Su, and G. L. Chen, “Microstructural control of TiAl–Nb alloys by directional solidification,” Acta Materialia, vol. 60, no. 2, pp. 498–506, 2012. View at: Publisher Site | Google Scholar
  14. M. Oehring, A. Stark, J. D. H. Paul, T. Lippmann, and F. Pyczak, “Microstructural refinement of boron-containing β-solidifying γ-titanium aluminide alloys through heat treatments in the β phase field,” Intermetallics, vol. 32, pp. 12–20, 2013. View at: Publisher Site | Google Scholar
  15. T. Klein, S. Niknafs, R. Dippenaar, H. Clemens, and S. Mayer, “Grain growth and β to α transformation behavior of a β-Solidifying TiAl alloy,” Advanced Engineering Materials, vol. 17, no. 6, pp. 1–5, 2014. View at: Google Scholar
  16. Z. Zollinger, V. Witusiewicz, A. Drevermann, D. Daloz, and U. Hecht, “Solidification of high Nb containing TiAl based alloys,” International Journal of Cast Metals Research, vol. 22, no. 1–4, pp. 339–342, 2009. View at: Publisher Site | Google Scholar
  17. X. Xu, L. Song, X. Jin, D. Han, X. Wang, and J. Lin, “Microstructure and microsegregation of directionally solidified Ti–45Al–8Nb alloy with different solidification rates,” Rare Metals, vol. 35, no. 1, pp. 70–76, 2016. View at: Publisher Site | Google Scholar
  18. M. Ganesan and D. Dye, “A technique for characterizing microsegregation in multicomponent alloys and its application to single-crystal superalloy castings,” Metallurgical and Materials Transactions A, vol. 36, no. 8, pp. 2191–2204, 2005. View at: Publisher Site | Google Scholar
  19. L. Song, X. J. Xu, J. Sun, and J. P. Lin, “Cooling rate effects on the microstructure evolution in the βo zones of cast Ti–45Al–8.5Nb–(W, B, Y) alloy,” Materials Characterization, vol. 93, pp. 62–67, 2014. View at: Publisher Site | Google Scholar
  20. C. Zhang, D. Ma, S. Kou, Y. A. Chang, and X. Y. Yan, “Microstructure and microsegregation in directionally solidified Mg–4Al alloy,” Intermetallics, vol. 15, no. 10, pp. 1395–1400, 2007. View at: Publisher Site | Google Scholar
  21. J. D. Hunt and S. Z. Lu, “Numerical modeling of cellular/dendritic array growth: spacing and structure predictions,” Metallurgical and Materials Transactions A, vol. 27, no. 3, pp. 611–623, 1996. View at: Publisher Site | Google Scholar
  22. A. F. Ferreira, J. A. Castroa, and L. O. Ferreira, “Predicting secondary-dendrite arm spacing of the Al-4.5wt%Cu alloy during unidirectional solidification,” Materials Research, vol. 20, no. 1, pp. 1–8, 2017. View at: Google Scholar
  23. W. Kurz and D. J. Fisher, Fundamentals of Solidification, Trans tech publications Ltd., Aedermannsdorf, Switzerland, 3rd edition, 1992.
  24. R. G. Santos and M. L. N. M. Melo, “Permeability of interdendritic channels,” Materials Science and Engineering: A, vol. 391, no. 1-2, pp. 151–158, 2005. View at: Publisher Site | Google Scholar
  25. V. T. Witusiewicz, A. A. Bondar, U. Hecht, and T. Y. Velikanova, “The Al–B–Nb–Ti system: IV. Experimental study and thermodynamic re-evaluation of the binary Al–Nb and ternary Al–Nb–Ti systems,” Journal of Alloys and Compounds, vol. 472, no. 1-2, pp. 133–161, 2009. View at: Publisher Site | Google Scholar
  26. A. E. Pontau and D. Lazarus, “Diffusion of titanium and niobium in bcc Ti-Nb alloys,” Physical Review B, vol. 19, no. 8, pp. 4027–4037, 1979. View at: Publisher Site | Google Scholar
  27. S. Y. Lee, O. Taguchi, and Y. Iijima, “Diffusion of aluminum in β-titanium,” Materials Transactions, vol. 51, no. 10, pp. 1809–1813, 2010. View at: Publisher Site | Google Scholar

Copyright © 2018 Xiangjun Xu et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

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