Upload
supersalvi
View
7
Download
0
Embed Size (px)
Citation preview
Effect of cooling rate on phase transformation in the low-carbonboron-treated steel
Di Zhang • Yoshiaki Shintaku • Shuichi Suzuki •
Yu-ichi Komizo
Received: 5 October 2011 / Accepted: 23 March 2012 / Published online: 11 April 2012
� Springer Science+Business Media, LLC 2012
Abstract In this research, phase transformation process
under different thermal cycles corresponding to a low and a
high heat input welding in the heat-affected zone of low-
carbon boron-treated steel is systematically investigated by
a high temperature laser scanning confocal microscopy. The
effect of thermal cycles on the phase transformation process
is quantified by measuring the transformation start tem-
perature of each transformation product and the average
number of nucleation sites of intragranular acicular ferrite.
Introduction
The variation of post-cooling rates alters the strength of
steel in association with toughness and formability [1–5].
This is achieved through ferrite grain refinement and
transformation of low temperature products. The micro-
structure changes from martensite (M) and/or intragranular
bainitic ferrite (IBF) at a higher cooling rate, to Wid-
manstatten ferrite (WF) and/or intragranular acicular ferrite
(IAF) at a medium cooling rate, and to intragranular
polygonal ferrite (IPF) and/or perlite (P) at a lower cooling
rate [6–8]. Among all the microstructures, IAF with a
chaotic arrangement of laths and fine-grained interlocking
microstructure toward optimizing strength and toughness
both in the weld metals and in the heat-affected zone
(HAZ). A large volume fraction of IAF in medium carbon
steel, low carbon steel, and medium carbon vanadium
steels were observed at cooling rates 10 [9], 5 [10, 11], and
0.1 K/s [12], respectively.
The optimal cooling rate for the formation of IAF also
depends on the chemical composition of the steels. Potent
inclusions for the formation of IAF are known as titanium-
rich cores (TiN, TiO, and Ti2O3) [13], alumina-rich cores
(Al2O3) [6, 7], crystalline galaxite spinel (MnAl2O4) [14],
boron-rich cores (BN, Fe2B and Fe23CB6) [15], and MnS
[6, 7, 13]. Segregation of boron and sulfur to the austenite
grain boundary (AGB) is also an effective way to improve
the formation of IAF.
The effect of cooling rate is generally investigated by
observing the microstructure at ambient temperature. In our
previous paper, we systematically investigated the effects
of boron content (0–33 ppm) and austenite grain size on
the formation of IAF in the HAZ of low-carbon boron-
treated steels [16]. Here, we focus on the effect of cooling
rate on the formation of IAF in these steels. A high tem-
perature laser scanning confocal microscopy (LSCM) is
used to directly observe the phase transformation process.
The effect of cooling rate is quantified by measuring the
average number of potent nucleation sites and the trans-
formation start temperature of each transformation product.
Experimental procedure
The chemical compositions of the low-carbon boron-treated
steels used in the present research are shown in Table 1. The
D. Zhang (&) � Y. Komizo
Joining and Welding Research Institute, Osaka University,
11-1 Mihogaoka, Ibaraki, Osaka 567-0047, Japan
e-mail: [email protected]
Y. Shintaku
Plate & Bar/Wire Rod Research & Development Department,
Sumitomo Metal Industries Ltd, 1-8 Fuso-cho, Amagasaki,
Hyogo 660-0891, Japan
S. Suzuki
Steel Sheet, Plate Titanium & Structural Seel Company,
Sumitomo Metal Industries Ltd, 8-11 Harumi 1-chome,
Chuo-ku, Tokyo 104-6111, Japan
123
J Mater Sci (2012) 47:5524–5528
DOI 10.1007/s10853-012-6444-9
contents of boron are 2 and 12 ppm in Sample 1 and Sample
2, respectively. The phase transformation processes were
directly observed using a high temperature LSCM and an
infrared imaging furnace (IIF), which was described in detail
in the previous research [17]. The materials for in situ
observation were machined into disks (5 mm diameter and
1 mm height) and mirror polished. The thermal cycles con-
sisted of three steps: (1) heating up to 1673 K, at 33 K/s, (2)
austenitizing at 1673 K for 5 s and 300 s, and (3) continu-
ously cooling to the ambient temperature, with different
cooling rates. The details of the thermal cycles are sche-
matically shown in Fig. 1. In the case of welding, the cooling
rate is also given by the cooling time from 1073 to 773 K,
Dt8/5 [18]. To simulate the cooling process in the high heat
input HAZ, Dt8/5 is chosen to be 4, 2, and 1 K/s for both
Sample 1 and Sample 2. The transformation start tempera-
ture of each transformation product and average number of
potent nucleation sites were directly measured from the in
situ microstructure.
Results and discussion
Figure 2 shows the austenite grain size measured at
ambient temperature for Sample 1 and Sample 2 for all
thermal cycles. The error bars are given on each data. The
figure shows that the austenite grain size increases with an
increase in holding time and a decrease in boron content.
The effect of cooling rate on the austenite grain size can be
neglected.
Table 1 Chemical compositions of the materials used in this paper (mass%)
C Si Mn P S Ti B N Al
Sample 1 0.15 0.20 1.49 0.006 0.002 0.010 0.0002 0.0050 0.004
Sample 2 0.15 0.19 1.47 0.006 0.002 0.010 0.0012 0.0051 0.005
0 400 800273
673
1073
1473
18735s
Thermal cycle 6
Thermal cycle 5
Thermal cycle 4
Time, s0 400 800
Thermal cycle 3
Thermal cycle 2
Time, s
Thermal cycle 1
300s
1673 1373 1373 1073 1073 773 773 473
Cycles 1 and 4 15 12 4 1
Cycles 2 and 5 10 7.5 2 0.5
Cycles 3 and 6 5 3.75 1 0.2
Temperature (K)
Cooling rate (K/s)
4K/s
Tem
pera
ture
, K
2K/s1K/s
4K/s 2K/s1K/s
Fig. 1 In situ thermal cycles set
by the IIF-controller system
1 2 4
Aus
teni
te g
rain
siz
e, μ
m
Cooling rate (Δ8/5) (K/s)
Sample 2
1 2 40
100
200
300
400
500
Cooling rate (Δ8/5) (K/s)
Sample 1
5s 300s
Fig. 2 Austenite grain size for
Sample 1 and Sample 2 under
all thermal cycles
J Mater Sci (2012) 47:5524–5528 5525
123
Figures 3 and 4 show the typical transformation prod-
ucts observed by in situ observation in the low-carbon
boron-treated steels. WF, also distinguished as WF side
plates or laths, first takes place at the AGBs and the pre-
existed grain boundary allotriomorphic ferrite (GBAF), and
grow into the austenite grain by sympathetic nucleation.
Another microstructure, IBFs, nucleate entirely in the
austenite grains. As shown in Fig. 3, IBF growth as intra-
granular needles or intragranular plates. IAFs, which
directly nucleated on the potent inclusions, contributed to
the formation of a fine-grained interlocking microstructure.
Transformation takes place both at the AGB and in the
austenite grain. The morphology of WF, IBF, and IAF were
detailed in our previous paper [16].
Figure 5 shows the transformation start temperatures of
WF, IBF, and IAF for Sample 1 and Sample 2 under all the
thermal cycles. The error bars for WF, IBF, and IAF are
given in the figure. With increasing holding time and
increasing boron content, the difference between the
transformation start temperatures of WF and IAF, expres-
sed by WF–IAF in the figure, decrease. The large area of
interface with smaller austenite grains is thought to have
induced a larger number of nucleation sites. With
increasing boron content, the boron segregation at the AGB
generally must have suppressed the transformation at the
AGBs. On the other hand, the formation of BN thin layer
on the TiN inclusions increased the potent of IAF nucle-
ation [16]. With increasing cooling rate, the transformation
start temperatures of WF, IBF, and IAF decrease. At the
same time, the difference of the transformation start tem-
peratures of WF and IAF decrease with increasing cooling
rate. It demonstrated that the potential for the formation of
IAF was greatly improved with increasing cooling rate. For
example, the transformation start temperatures of WF and
IAF of Sample 2 with a holding time of 300 s and a cooling
rate Dt8/5 of 4 K/s were almost the same. The experimental
50μm
50μm 50μm
IAF
(a)972K
(d)925K (e)900K
50μm 50μm
50μm
(b)951K (c)940K
(f)Final microstructure
IAF nucleationInclusion IAF
IAF
IAF
IAF
Fig. 4 IAF observed by in situ
observation. (Sample 2 under
thermal cycle 1)
200μm
200μm
IBF
WFWF
IBF
(a)994K
(d)959K (e)935K
Austenite grain boundary
Inclusion
IBF nucleation Growth of IBF
WF
WF
200μm
200μm
200μm
200μm
(b)978K (c)966K
(f)Final microstructure
WF
Fig. 3 WF and IBF observed by in situ observation. (Sample 2 under thermal cycle 4)
5526 J Mater Sci (2012) 47:5524–5528
123
results of Sample 1 and Sample 2 are also presented in the
continuous cooling transformation (CCT) diagrams, as
shown in Fig. 6. Sample 2 with a holding time of 300 s and
a cooling rate Dt8/5 of 4 K/s had the highest nucleation
potency of IAF.
Figure 7 shows the average number of potent nucleation
sites under all the thermal cycles for both Sample 1 and
Sample 2. The measured average number of potent
nucleation sites for Sample 1 was almost the same. While
for Sample 2, the nucleation sites increased with increasing
WF IBF IAF WF-IAF
Transformation start temperature
273
303
963
993
1023
Tem
pera
ture
, KTe
mpe
ratu
re, K
273
303
963
993
1023
Sample 1 5s
1 2 4
Cooling rate (Δ8/5)(K/s)
Sample 1 300s
Sample 2 5s
1 2 4
Sample 2300s
Cooling rate (Δ8/5)(K/s)
Fig. 5 Transformation start
temperatures of WF, IBF, and
IAF for Sample 1 and Sample 2
under all thermal cycles
0 200 400 600
Time, t/s
300s
2K/s
5s
1K/s 1K/s2K/s4K/s4K/s
IAFIAF
IBFIBF
WFWF
Sample 2
0 200 400 600923
948
973
998
1023
Time, t/s
300s
2K/s
5s
1K/s 1K/s2K/s4K/s4K/s
IAFIAF
IBFIBF
WFWF
Sample 1
Tem
pera
ture
, K
Fig. 6 CCT diagrams of
Sample 1 and Sample 2
1 2 40.0
0.2
0.4
0.6
0.8
Num
ber
of n
ucle
atio
n si
tes,
/104 μm
2
5s 300s
1 2 4
Cooling rate (Δ8/5) Cooling rate (Δ8/5)
Sample 1 Sample 2
(K/s) (K/s)
Fig. 7 Average number of
nucleation sites of IAF for
Sample 1 and Sample 2 under
all thermal cycles
J Mater Sci (2012) 47:5524–5528 5527
123
cooling rate. Sample 2 with a holding time of 300 s and a
cooling rate Dt8/5 of 4 K/s had the highest number of potent
nucleation sites.
Conclusion
In general, small austenite grain promotes the grain
boundary transformation. While large austenite grain and
higher content of boron bring high number of potent
nucleation site. Increasing cooling rates result in the lower
transformation temperatures. In the boron-treated steel, at a
given austenite grain size and boron content, increasing
cooing rate (from Dt8/5 = 1 to Dt8/5 = 4 K/s) is possible to
switch the microstructure from grain boundary nucleation
(GBAF and WF) to intragranular nucleation (IBF and IAF).
It also should be pointed out that the optimal cooling rate
for the formation of IAF depends on the boron content and
the austenite grain size of boron-treated steels. In the
present research, the sample with an appropriate boron
content (12 ppm) and higher holding time (300 s) under a
proper cooling rate Dt8/5 = 4 K/s) shows the optimized
microstructure. The presented results show that the high
temperature in situ observation is able to quantitatively
investigate the phase transformation process in real time.
References
1. Shanmugam S, Ramisetti NK, Misra RDK, Mannerring T, Panda D,
Jansto S (2007) Mater Sci Eng A 460–461:335
2. Ghosh A, Das S, Chatterjee S, Ramachandra P (2006) Mater
Charact 56:59
3. Ai JH, Zhao TC, Gao HJ, Hu YH, Xie XS (2005) J Mater Proc
Tech 160:390
4. Fang X, Fan Z, Ralph B, Evans P, Underhill R (2002) Mater Sci
Technol 18:47
5. Thompson M, Ferry M, Manohar PA (2001) ISIJ Int 41:891
6. Sarma DS, Karasev AV, Jonsson PG (2009) ISIJ Int 49:1063
7. Babu SS, Bhadeshia HKDH (1990) Mater Sci Technol 6:1005
8. Shibata K, Asakura K (1995) ISIJ Int 35:982
9. Madariaga I, Gutierrez I, Garcia-de Andres C (1999) Scr Mater
41:229
10. Shim JH, Cho YW, Chung SH (1999) Acta Mater 47:2751
11. Byun JS, Shim JH, Suh JY (2001) Mater Sci Eng A 319–321:326
12. Ishikawa F, Takahashi T, Ochi T (1994) Metall Mater Trans A
25A:929
13. Zhang D, Terasaki H, Komizo Y (2010) Acta Mater 58:1369
14. Yamada T, Terasaki H, Komizo Y (2008) Sci Technol Weld Join
13:118
15. Koseki T, Thewlis G (2005) Mater Sci Technol 21:867
16. Zhang D, Shintaku Y, Suzuki S, Komizo Y (2012) Metallur
Mater Trans A 43A:447
17. Komizo Y, Terasaki H, Yonemura M, Osuki T (2008) Weld
World 52:56
18. Barbaro FJ, Kraulis P, Easterling KE (1989) Mater Sci Technol
5:1057
5528 J Mater Sci (2012) 47:5524–5528
123