admin管理员组文章数量:1532140
2023年12月12日发(作者:)
Formulation
Hot Rolling
of Static
Process
Recrystallization
of Steel Plate*
of Austenite
inBy Atsuhiko YOSHIE,** Hirofumi MORIKAWA,** Yasumitsu
and Kametaro ITOH***Synopsis
A critical condition for static recrystallization of austenite (r) in plate
rolling process has been formulated in terms of the change in average dis-location density. The latter was calculated from the decrease in stress
due to recovery and recrystallization observed by the double deformation
tests. The main results are summarized as follows:
(1) The relation among stress, strain and average dislocation density
has been formulated. By the present formulation, deformation stress for
practical conditions of the controlled rolling of plate can be calculated as
a function of temperature, strain, strain rate and r grain size.
(2) The behavior of static recovery and recrystallization taking place
during holding period after deformation has also been formulated as a
function of dislocation density. This formulation makes it possible to
estimate the critical condition for static recrystallization during an interval
time between the successive rolling passes of plate.
(3) Deformation conditions such as temperature, strain, strain rate,
Y grain size and interval time between passes affect the critical condition
for recrystallization. The shorter interval time elevates the temperature
limit of non words: hot deformation; static recrystallization; austenite; plate
rolling; incubation time; mathematical **I. Introduction
Controlled rolling process has become one of the
important processes in steel plate production. Espe-cially the total reduction in the temperature range of
non recrystallization has been increased for improving
the mechanical properties. Therefore, it is indis-pensable for the process design to make clear the
critical condition for recrystallization of austenite
(r) in hot rolling.
As seen in the schematic illustration of Fig. 1, the
critical condition for static recrystallization of r is
considered to be a function of temperature, stored
strain, strain rate in rolling and r grain size as well
as chemical compositions of steels. In higher tem-perature range, the critical strain (&cr) for recrystalliza-tion is smaller than the strain in each pass of com-mercial plate rolling. As a result, recrystallization
starts during the interval time before the next pass.
In lower temperature range, however, recrystalliza-tion does not begin until an accumulated strain of
several passes exceeds ~cr because the strain of each
rolling pass does not usually exceed 8er.
The critical conditions for recrystallization have
been investigated by many authors. Some authors'-3>
have observed the microstructure of steels quenched
after hot rolling and shown the maps of rolling condi-*
tions which are divided into recrystallization range
and non recrystallization range. This method, how-ever, requires the growth of recrystallized grains to
observable size to define the onset of recrystallization,
so the observed start of recrystallization may be
apparent and different from its true start (i.e., nuclea-tion). Moreover, when a lower hardenability steel
is employed or a specimen is heavily deformed, it is
difficult to discern prior r grain structure because
quenched r transforms to martensite insufficiently.
For these reasons, the critical condition derived from
microstructural observation might not be accurate.
Other authors4,5~ have performed the double defor-mation tests and reported an empirical criterion of
recrystallization : a value of softening ratio specified
at the inflection in a softening ratio res. time curve.
However, the physical meaning of the specific value of
softening ratio in this method is indefinite. Recently
some authors6-$~ have formulated mathematically
the behavior of recrystallization in hot rolling process
in terms of the changes in observed microstructure.
The critical condition for static recrystallization, how-ever, was not described quantitatively, because theFig.1. Schematic illustration of the critical conditions for
recrystallization of Y in hot rolling process (on
assumption that chemical composition, strain rate
and austenite grain size are constant).Based on the paper presented to the 110th ISIJ Meeting, October 1985, 51500, at Niigata University in Niigata. Manuscript
received on August 29, 1986; accepted in the final form on March 13, 1987. © 1987 ISIJ
* * Plate, Bar, Shape & Wire Rod Research Laboratory, R & D Laboratories-II (stationed at Higashida), Nippon Steel Corporation,
Edamitsu, Yahatahigashi-ku, Kitakyushu 805.
* * * Plate Technical Division, Nippon Steel Corporation, Otemachi, Chiyoda-ku, Tokyo chArticle(425)(426) Transactions ISIJ, Vol. 27, 1987incubation period of recrystallization was not taken
into account in their calculation.
In the present report the critical condition for
recrystallization in hot rolling process has been
expressed in a mathematical model by taking the
incubation period into consideration. The model
has been derived not from the change in observed
microstructure but from the decrease in the stress
observed in the present double deformation tests.
In order to estimate the critical condition, the
observed stress has been related to the average dis-location density (p) because the relations among
p, strain and
authors.7'9"°>stress have been clarified by many
II. Mathematical Model
1. Procedure of Mathematical Analysis
Figures 2(a) and 2(b) shows a schematic illustra-tion of the changes in average dislocation density
and stress-strain curves in double deformation tests. 11)
Average dislocation density increases with deforma-tion and decreases during interval time due to the
progress of recovery and recrystallization.
assumption that stress (a) corresponds to p, the value
On the
of p at each point (for example, point A or B in Fig.
2(a)) can be calculated from the observed j (for ex-ample, stress-strain curves A or B in Fig. 2(b)).
Senuma et al. 12) formulated deformation resistance
of hot strip steel as a function of p. At the 1st step
of the present analysis, the relation between r and
p is formulated in the same way.
the decrease in p due to recovery and recrystallization
At the 2nd step,
is formulated as a function of time after deformation
including undetermined coefficients. At the 3rd step,
the values of undetermined coefficients are determined
from the decrease in p during interval time calculated
through the observed a in double deformation tests.
With these procedures, progress of recovery and recrys-tallization after deformation is formulated mathe-matically. The schematic illustration of the pro-cedures of analysis is also shown in Fig. 2.
2. Relation among Deformation Stress, Strain and Average
Dislocation Density
Deformation stress during hot working is expressed
as
a = a'id+ae .........................(1)
where a'id is an internal stress and oe is an effective
stress. As the latter term can be neglected when r
is deformed at high temperature,9> the relation be-tween a and p is expressed as10)
a ale = ap1~2, .. ...................(2)
where a is a constant.
Next, the relation between strain (e) and p will be
derived. Strain hardening and dynamic recovery
proceed simultaneously with hot deformation.
change in p is formulated into the following differential
The
equation.
dp = (op/or)dr+(op/ot)dt ..................(3)Fig. 2. Schematic i
llustration ofthe procedure of the the rolling strain of plate is relatively small, p is
assumed to be proportional to E.13) Therefore the rate
of strain hardening (op/oe) is expressed as
op/or=b ............................(4)
where b is a function of temperature ( T)9) and
b = b° exp (Qb/RTT) ...................(5)
where b° : a constant, Qb : an apparent activation
energy and R : the gas constant (8.314 J. mol-1 K-1).
Dislocation configuration corresponds to e and multi-plication of dislocation depends on T.
of strain rate (s) and r grain size (Dr) are neglected
The effect
because their contributions are assumed to be small.
The rate of dynamic recovery is expressed as14)
op/ot = -cpn .........................(6)
where c is a function of T, and Dr, C coDrae s exp (Qe/RT) ~ ...............( )
where co, me and ne are constants, and Qe an apparent
activation energy. The effect of D1 and are assumed
to be expressed in the form of power function because
their dependence on c is not clear. On the same
assumption, the similar functional forms are adopted
in Eqs. (10), (14) and (15), which will be discussed
below. The opportunity for annihilation of disloca-tions with opposite Burgers-vector (n=2 in Eq. (6))
is very few because dislocations hardly cross-slip in
< crystal.15) Therefore dislocation can annihilatemainly due to climbing and absorption at grain
boundary (n=1 in Eq. (6)). With the combination
of Eqs. (4) and (6) with n=1, the relation between
p and
deformation asis formulated for a constant through the
p = b/c(1 _ e-eE)+ po e-eE(8)where po is the dislocation density of annealed steel.
From Eqs. (2) and (8), stress-strain relations of any
deformation conditions of the controlled rolling of
plate in r temperature range can be calculated.3. Relation between Static Recovery and Average
Disloca- tion Density
The annihilation rate of p during static
recovery
after deformation is expressed in the same
form asthat of dynamic recovery as14)op/ot = -d .p ,(9)where t is time after deformation andd = doDmdEnd exp (Qd/RT) ,(10)where do, and and nd are constants, and Qd an apparent
activation energy. When p =Pd at t = 0 and p = po at
t=oo, the relation between p and t is formulated intop = (pd-po) eXp (-d •t)+po ,(11)where pd is a dislocation density just after hot defor-mation.4. Relation between Static Recrystallization and Average
Dislocation Density
After static recrystallization starts at t = z (z : incu-bation period), p decreases according to Eq. (12) due
to progress of recrystallization and becomes po after
recrystallization completes.p = (po-pr)X +pr ,(12)where X is the fraction recrystallized, and pr is the
dislocation density according to Eq. (11). The
value of X is expressed as a function of t into the
following equation. 16)X =1-exp {-e(t-z)'),(13)where e is a function of T, e, and Dr as in the form ofe = eo DmeBne gee exp (Qe/RT),(14)TransactionsIs",Vol.27,1987(427)where eo, me, ne and le are constants, and Qe an ap-parent activation energy.
function of T, e, s and Dr, asIncubation period, z, is a
T =-ODmTEnv&z exp (QTIRT),(15)where z-o, mt, nz and l= are constants, and Q an
apparent activation energy. The value of n in
Eq. (13) is assumed to be a constant value of 2, on
the basis of the present experimental data and the
report of other authors.7,17)
By substitution of Eq. (13) into Eq. (12), the
relation among p, e, t and z is obtained. By expand-ing the term of t and z into series and neglecting
the terms of higher order after twice logarithmic
calculation, it is possible to obtain a linear equation
of p, e, t and z-. The values of e and z are determined
by regression analysis with the series of p calculated
from the observed stress at s=0.05 (a o o5) in the
2nd pass of double deformation tests in. which T, ~,
and DY are constant and t a variable. The constants
included in Eqs. (14) and (15) are also obtained by
regression analysis with the calculated e and z for
different T, a, E and Dr.
With the combination of the equations mentioned
above, static recovery and recrystallization behavior
and the critical condition of recrystallization can be
calculated. This mathematical model can be applied
to multi-pass rolling, because p can be calculated
consistently from the beginning to the end of rolling
. Materials and Experimental Methods
The chemical composition of steels used are shown
in Table 1. The high hardenability steel A contain-ing Ni, Mo and B was employed for the comparison
between microstructure and deformation stress and
Nb steel B was employed for this formulation which
was a typical steel for plates produced by controlled
rolling. Single or multi deformation tests were
performed by using a compression type hot deforma-tion simulator. 18) Specimens were machined from
continuous casting slabs to the column with a size
of 7 mm diameter and 12 mm height.
The specimens were heated in an induction furnace
to the heating temperature (HT) at a heating rate of
5°C/s, and held for 10 min followed by cooling to
each deformation temperature (DT) at a cooling rate
of 5°C/s. The fluctuation of temperature in the speci-men is proved to be within 5°C during heating and
cooling and within 2°C during holding. Then single
or multi axial compressions were performed at DT
immediately. Strain, deformation speed, interval
time during deformation and temperature were
precisely
case of double deformation test, stress-strain curves
controlled through a computer. In the
of the 2nd pass were measured just after holding time
ranging 1 1 000 s after the 1st pass. The prior r
grain boundaries were observed in some specimens
quenched just after the same holding chArticle (428)TransactionsISIJ,Vol.27, 1987Table alcompositionsof thesteels.(wt%) y-v.v
Fig.3. Progress of recrystallization duringintervaltime after the1st deformation.1 V, Results
1. Comparison between Microstructure and Deformation
Stress
Steel A was employed for the observation of the
prior
after deformation.
r grain boundaries
Figures 3 and 4 are the optical
of a quenched specimen
microstructures of the quenched specimens and the
observed stress-strain curves, respectively. These
figures show the decrease in deformation stress in the
2nd pass due to the progress of recrystallization.
Figure 5 shows the relation among the time after the
1st pass, the fraction of r recrystallized, X, and
6E-0.05 of the 2nd pass. The value of X was measured
from the micrographs. Figure 5 reveals that the
decrease in a for t < 10 s is caused by recovery and that
for t >_ 10 s by recovery and recrystallization. From
these data, however, it is impossible to determine
exactly the true start of recrystallization as mentioned
before.
2. Formulation of Recovery and Recrystallization Behavior
of 0.01 % Nb Steel
Steel B was employed for this formulation. Table
2 shows the experimental conditions used.
Chemical analysis of the specimens quenched just
after holding for 10 min at the heating temperature
ranging 95O- 1 200°C confirmed that Nb was com-pletely
HT is considered to affect Q only through Dr.
dissolved even at HT=950°C. Therefore
In
this experiment, Dr varied from 12.5 to 300 sm
according to HT from 950 to 1 200°C. The possible
effect of Nb precipitation on ~E=0,05 by holding at a
certain temperature before deformation was also
investigated. Its effect, however, was very small
because both C and Nb contents were relatively small N 4 V Ul F i, i 1 1 ~ l Ig V V ~, L 1 ~ V V V VI, C~ V. V A7
Fig.4. Variation of stress-strain curves with interval . 5.
Effect of interval time on 0,=O.05 and X.
Table 2. Experimental conditions for steel the steel B. Therefore precipitation hardening
can be neglected and only strain hardening is caused
by retardation of recovery and recrystallization
through the variation of 6 with Nb.
The constants included in Eqs. (2), (5) and (7)
were obtained by regression analysis mentioned
before. The units of observed data are kg/mm2 for
Q and sm for Dr. Table 3 shows the values of con-stants. The effect of Dr, m~ and ~, n~ on the rate of
dynamic recovery are relatively small. The depen-dence of DT on deformation resistance which is usuallyTransactionsISIJ,Vol.27,1987(429)Table nts for Eqs.(2), (5), (7), (10), (14) and (15)for steel sed as Misaka's type equation'9> is divided into
the dependence of strain hardening, Qb and that of
dynamic recovery, Q~ . As these values are of the
same order of magnitude but of the opposite sign,
7 increases with decrease in DT. The values of
constants included in Eqs. (10), (14) and (15) are
also shown in Table 3. The effect of Dr, and and
~, nd are also small on the progress of static recovery.
The effect of ~, l~ on the progress of recrystallization
is by far larger than that of Dr and E. The value of
l3 is close to that of experimental formula by the
other author.20~3. Comparison between Experimental Data and Calculated
Results
Figure 6 shows the stress-strain curves of various
deformation conditions. Calculated results by using
Eqs. (2)' (8) are in good agreement with the experi-mental data in every case. Figure 7 illustrates the
decrease in ~E=0.05 at the 2nd pass due to the progress
of recovery after deformation. Calculation was per-formed on assumption that only recovery progressed.
Experimental data are consistent with the calculated
results before the start of recrystallization and deviate
with the progress of recrystallization. In the lower
DT, Fig. 7(a), the incubation period for recrystalliza-tion is considered to be between 20 and 100 s for
=0.2 and between 10 and 20 s for a=0.4. In the
higher DT, Fig. 7(b), recrystallization starts in much
shorter period after deformation. Figure 7 reveals
that the larger e and the higher DT result in the
shorter incubation period.
Figure 8 shows the decrease in cr, 0,05 due to
recovery and recrystallization during holding time
after deformation. The progress of both recovery
and recrystallization were calculated in this case.
Lines and solid triangles represent calculated results
from Eqs. (11), (12) and (15). Good agreement
between experimental data (open marks) and calcu-lated results proves that this mathematical model is
effective to estimate the recovery and recrystalliza-tion behavior in plate rolling process.V. DiscussionFig. 6. Effect of FIT, DT, and Eon . 7. Decrease
to recovery
in deformation
of in
the 2nd pass due1. Effect of Nb on Deformation Stress
The decrease in observed stress between the 1st
and the 2nd pass arises from the difference between
softening due to recovery and recrystallization and
precipitation hardening of Nb. Their contributionFig. 8. Decrease
to recovery
in deformation stress in the 2ndpass dueand chArticle(430 Transactions ISU, Vol. 27, 1987can not be discerned because of their interactions.
Figure 9 shows the effect of Nb content on a E-0.05
obtained by the single deformation test of 0.10%C-1.00%Mn steel. The stresses of specimens held for
500 s at 800°C for precipitation before the deforma-tion were nearly equal to the stresses of the specimens
without holding. From Fig. 9, stress increment is
proportional
solution hardening.
to the Nb content in accordance with
As the present specimen con-tains only 0.01 % Nb, the precipitation hardening is
expected to be no more than 1 kg/mm2, which is
within the error of observed stress.
Precipitation behavior of Nb(CN) may differ
before and after deformation.21~ In this respect,
DeArdo et al.22~ reported that Nb (CN) selectively
precipitates at grain boundary and subgrain boundary
of 1'. Therefore the effect of these precipitates on
deformation stress might be negligibly smaller than
that of coherently precipitated Nb(CN) in matrix.
Though the precipitation hardening of Nb(CN) is
neglected in the present model, experimental data
are consistent with the results of calculations.
2. Critical Condition of Recrystallization after Deformation
Incubation period, z, is calculated as a function
of ~, 7 and Dr in Eq. (15). As a result, effect of
deformation conditions on the critical conditions for
recrystallization can be analyzed by Eq. (15). Figure
10 shows the effect of 6 on z. In the multi-stage defor-mation test, s in the abscissa is the stored strain
calculated with Eq. (8). Calculated results indicate
that the higher DT and the smaller Dr result in the
shorter incubation period. Figure 11 shows the crit-ical conditions for static recrystallization of r. The
right upper sides of the lines are the recrystallization
ranges and the left lower sides are the non recrystal-lization ranges. If an interval time between defor-mation is longer than the incubation period (param-eter in Fig. 11), recrystallization starts during the
interval time. Therefore a short interval time elevates
the temperature limit of non recrystallization. Figure
12 shows the relation between applied deformation
strain and stored strain at the start of recrystallization.
The difference between these strains indicates the
decrease in dislocation density due to recovery during
the incubation period. Figure 13 shows the effect
of s on the softening ratio (S) in double deformationFig. of Nb content on a,_o.o5 in the1st just at the start of recrystallization. The ratio
S is described as
S = (Um-6n)I(~m-~0) ................ (16)
where 6,n is the peak stress in the 1st pass, and o and
7 fl are the yield stress of the 1st and 2nd passes,
respectively. These stresses are calculated from Eqs.
0'n were taken as 6f-o(2), (8), (11) and (15). In the calculation, 6o and
respectively. Djaic and Jonas,4~ and Ouchi et a1.5~
.o5 for the 1st and 2nd pass,
reported that static recrystallization started at a
specific value of S, O.20'0.30. As the strain at the
1st pass were 0.14 or 0.20 respectively in their experi-ments, the values of S calculated by the presentt model
are nearly 0.2-'0.3. From Fig. 13, however, the
value of S changes widely with the variation of
deformation conditions. A general criterion of recrys-Fig. of strain . alconditions for recrystallizationof . 12. Comparison between applied
deformation strain
and stored strain at the start of .13. Effect of deformation conditions on softening ratio
at the start of ation is not necessarily described in terms of
a specific value of S. On the other hand, the present
model predicts satisfactorily the critical condition of
recrystallization for comprehensive conditions of hot
rolling of . Conclusion
The critical condition of static recrystallization of
r in plate rolling process has been formulated in terms
of the change in average dislocation density calculated
from the decrease in deformation stress due to recovery
and recrystallization in the double deformation tests.
The results are summarized as follows :
dislocation
(1) The relation among stress, strain and average
density and the change in dislocation
density due to strain hardening and dynamic recovery
during deformation have been formulated. By the
present formulation, the deformation stress for prac-tical deformation conditions of controlled rolling canTransactionsISIJ,Vol.27,1987(431)be calculated as a function of temperature, strain,
strain rate and r grain size.
lization during holding period after deformation has
(2) The behavior of static recovery and recrystal-also been formulated as a function of dislocation
density. This formulation successfully predicts the
critical condition of recrystallization during the inter-val time between the successive rolling passes of plate.
strain rate, r grain size and interval time between
(3) Deformation conditions such as temperature,
passes affect the critical condition of recrystallization.
A smaller interval time elevates the temperature
limit of non recrystallization.
tallization such as a specific value of softening ratio
(4) An empirical criterion for the start of recrys-is not always valid, because the softening ratio
changes largely with deformation conditions.
Acknowledgements
The authors wish to thank Dr. H. Sekine, Dr. H.
Mimura and Dr. T. Senuma, Nippon Steel Corp.,
for their helpful NCES
1) H. Sekine, T. Maruyama and Y. Kawashima: Proc. Int'1
Conf. on Thermomechanical Processing of Microalloyed
Austenite, AIMS, Pittsuburgh, (1982), 141.
2) T. Tanaka, N. Tabata, T. Hatomura and C. Shiga: Micro- alloying 75, Union Carbide, New York, (1977), 88.
3) I. Kozasu, C. Ouchi, T. Sanpei and T. Okita : Micro- alloying 75, Union Carbide, New York, (1977), 120.
4) RAP. Djaic and J.J. Jonas: JISI, (1972), 256.
5) C. Ouchi, T. Okita, T. Ichihara and Y. Ueno : Trans.
ISIJ, 20 (1980), 833.
6) C. M. Sellars: Sheffield Int'1 Conf. on Working and
Forming Process, London, (1979), 3.
7) T. Senuma, H. Yada, G. Matsumura and T. Futamura:
Tetsu-to-Hagane, 70 (1984), 2112.
8) Y. Saito, M. Kimura, Y. Tanaka, T. Sekine, K. Tsubota
and T. Tanaka: Kawasaki Steel Giho, 15 (1983), 241.
9) T. Touma, H. Yoshinaga and S. Morozumi : J. Japan Inst.
Met., 38 (1974), 170.
10) J. E. Bailey and P. B. Hirsch : Phil. Mag., 5 (1960), 485.
11) A. Yoshie, Y. Onoe, T. Fujii, T. Terazawa and T. Senuma:
Tetsu-to-Hagane, 71 (1985), 51500.
12) T. Senuma, H. Yada, G. Matsumura, S. Hamauzu and K.
Nakajima : Tetsu-to-Hagane, 70 (1984), 1392.
13) W. G. Johnston and J. J. Gilman: J. Appl. Phys., 30
(1959), 129.
14) R. Sandstrom: Acta Met., 25 (1977), 897.
15) S. Suzuki : Strength of Metal, AGNE, Tokyo, (1981),
154.
16) J. W. Chan: Acta Met., 4 (1956), 449.
17) D. R. Barraclough and C. M. Sellars: Metal Sci., 13
(1979), 257.
18) T. Terazawa, A. Yoshie, Y. Onoe and K. Nakajima :
Tetsu-to-Hagane, 69 (1983), 5631.
19) Y. Misaka and Y. Yoshimoto: J. Japan Soc. Technol. Plast.,
8 (1967), 414.
20) S. Licka, L. Zela, E. Piontek, M. Kosar and T. Prnka:
Proc. Int'l Conf. Steel Rolling, ISIJ, Tokyo (1980), 840.
21) B. Dutta and C. M. Sellars: Mater. Sci. Technol., 2 (1986),
146.
22) A. J. DeArdo, J. M. Ray and L. Mayer: Proc. Int'1
Symp. on Niobium, AIME, San Francisco, (1981), 685.
版权声明:本文标题:计算变形条件下的位错密度演化,应力,应变,位错关系。经典的公式,外文文 内容由热心网友自发贡献,该文观点仅代表作者本人, 转载请联系作者并注明出处:https://m.elefans.com/xitong/1702393919a4727.html, 本站仅提供信息存储空间服务,不拥有所有权,不承担相关法律责任。如发现本站有涉嫌抄袭侵权/违法违规的内容,一经查实,本站将立刻删除。
发表评论