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Microstructure Evolution in Fine-Grained Microalloyed Steels
K.R. Lotteya and M. Militzerb
The Centre for Metallurgical Process Engineering
The University of British Columbia
Vancouver, BC Canada V6T [email protected], [email protected]
Keywords: Microstructure, Fine-grained steel, Continuous cooling, Ferrite, Transformation,Modeling Abstract. There is an increasing emphasis to develop novel hot-rolled high strength steels with
fine and ultra fine grain sizes for structural and other applications. Traditionally the concept of
microalloying has been employed to refine microstructures thereby obtaining increased strength
levels. For example, employing an alloying strategy with Nb, Ti and Mo is promising to attain
yield strength levels of 700MPa and beyond. In the present study, the transformation behaviour is
investigated for a HSLA steel containing 0.05wt%C-1.65wt%Mn-0.20wt%Mo-0.07wt%Nb-
0.02wt%Ti. The ferrite formation from work-hardened austenite has been studied for simulated
run-out table cooling conditions employing a Gleeble 3500 thermomechanical simulator equipped
with a dilatometer. The effects of cooling rate and initial austenite microstructure, i.e. austenite
grain size and degree of work hardening, on the austenite decomposition kinetics and resulting
ferrite grain size have been quantified. Based on the experimental results, a phenomenological
transformation and ferrite grain size model is proposed for run-out table cooling conditions. The
transformation model includes submodels for transformation start and ferrite growth. The latter is
described using a Johnson-Mehl-Avrami-Kolmogorov approach. The degree of work hardening isincorporated by introducing an effective austenite grain size as a function of the strain applied
under no-recrystallization condition. The ferrite grain size can be predicted as a function of the
transformation start temperature. Increasing both cooling rate and amount of work hardening can
optimize ferrite grain refinement. In the present steel, ferrite grain sizes of as low as 2µm have
been obtained in this way. The results observed for the present steel are compared to the
transformation behaviour in previously studied Nb-Ti HSLA steels of similar strength levels.
Introduction
There is an increasing demand to develop novel hot-rolled high strength steels with superior
properties such as improved strength and toughness which has resulted in numerous investigationsof steel chemistry and thermomechanical processing. For example, the pipeline industry requires
linepipe grades with increased strength levels, i.e. X100 and X120 [1]. One approach in this regard
has been to develop novel microalloyed steels with refined microstructures that lead to increased
strength levels. In a hot mill the final microstructure and, thus, the properties of the hot-rolled steel
are a function of the austenite decomposition and precipitation that occur during cooling and
coiling. Accelerated cooling on the run-out table in combination with finish rolling under no-
recrystallization conditions is a key processing step for developing the desired resulting fine and
ultra fine grained ferrite microstructure [2].
To design and control novel processing routes, microstructural engineering has gained
significant attention in recent years with the development of predictive tools that quantitatively link
the process parameters with the final properties of hot-rolled steel [3][4]. Such process models
Materials Science Forum Vols. 500-501 (2005) pp. 347-354online at http://www.scientific.net © (2005) Trans Tech Publications, Switzerland
All rights reserved. No part of contents of this paper may be reproduced or transmitted in any form or by any means without thewritten permission of the publisher: Trans Tech Publications Ltd, Switzerland, www.ttp.net. (ID: 64.76.110.6-26/02/07,18:53:25)
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currently exist for plain carbon and a number of high strength low alloy (HSLA) steels of up to
550MPa minimum yield strength [4].
The present paper extends previous modeling work for the austenite-to-ferrite transformation to
a microalloyed low-carbon steel with a minimum yield strength of 620MPa. The required model
parameters are obtained from experimental transformation studies for cooling conditions similar to
those found on the run-out table of a hot-strip mill.
Experimental
Methods. The steel investigated was supplied by IPSCO Inc as hot-rolled transfer bar material.
The chemical composition of the steel is given in Table 1. The A e3 temperature of this steel
chemistry is 821oC as obtained by Thermo-Calc software version N utilizing the Fe2000 database.
Table 1 - Steel Composition [wt%]
C Mn Al Si Cu Mo Ni Nb Ti S P
0.05 1.65 0.027 0.025 0.29 0.196 0.16 0.071 0.021 0.004 0.01
In order to establish the parameters required for the overall transformation model, laboratory
experiments were carried out on a Gleeble 3500 thermomechanical simulator equipped with a
dilatometer. Details of the test procedures are described in a previous paper [5]. First, reheat tests
were performed in order to establish suitable austenitization conditions for subsequent
transformation tests. The selected austenitization conditions and the resulting austenite grain sizes,
d γ , are summarized in Table 2 where d γ is reported as the equivalent volumetric grain size which is
required for modeling purposes. To obtain the equivalent volumetric grain size the measured
equivalent area diameter was multiplied by 1.2 [6].
Table 2 - Heat Treatment Schedules* and Austenite Grain Sizes
Holding Temperature [oC] Holding Time [s] d γ [µm]
950 120 14
1050 120 32
1150 120 53
*A heating rate of 5°C/s to reach the holding temperature was employed in all schedules.
Double-hit axisymmetric compression tests were conducted in another series of tests in order to
establish conditions that introduce retained strain in the initial austenite microstructure, i.e.
pancaked austenite, which reflect the microstructure at the exit of the finishing mill. In order toobtain pancaked austenite the compression tests were carried out at a deformation temperature of
850oC where for a holding time of 15s and the largest prestain of 0.5, the softening remained below
20%. A softening of 20% or lower is assumed to be indicative that just recovery but no
recrystallization has occurred [7].
Austenite decomposition was investigated during continuous cooling with and without prior
deformation of austenite. Continuous cooling transformation (CCT) tests were conducted to
dilatometrically quantify the austenite decomposition kinetics as a function of initial austenite
microstructure and cooling rate, ϕ , which was calculated at the Ae3 temperature. Microstructures
were revealed using standard metallographic procedures.
Results. Figure 1 gives examples of microstructures obtained in the CCT tests with d γ =14µm.
Comparing Figure 1a) with 1c) and 1b) with 1d), respectively, shows that a refinement in themicrostructure was observed as a result of accelerated cooling. In case of tests without
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deformation, see Figures 1a) and 1c), a transition from polygonal ferrite-pearlite to non-polygonal
transformation products, such as bainite, was observed with accelerated cooling. The effect of
retained strain on the final microstructures is to promote the formation of polygonal ferrite and to
refine the ferrite microstructure, see e.g. Figures 1c) and 1d). The effects of pancaking austenite in
combination with accelerated cooling on the final microstructure are clearly seen by comparing
Figures 1a) and 1d) where a significant refinement in the ferrite microstructure is evident. Themeasured polygonal ferrite grain sizes at various cooling rates and strain levels are shown in Figure
2. Significant ferrite grain refinement of approximately 2µm was achieved with the application of
accelerated cooling and deformation, i.e. the finest ferrite grain size of 2.1µm was attained with the
largest strain of 0.5 and accelerated cooling at 88oC/s while a ferrite grain size of 4µm was
measured from slow cooling at 1oC/s with no retained strain. Similar trends were also observed for
the larger austenite grain size of 32 and 53µm. These tendencies are similar to those observed in
previously studied HSLA steels [8].
While both increase of cooling rate and increase of retained strain leads to grain refinement in
the final microstructure their effect on transformation temperatures are opposite. Increasing the
cooling rate decreases transformation temperatures while increasing the retained strain increases
transformation temperatures. For example, considering the transformation start temperature, T S , in
CCT tests for d γ =53µm, the following was observed: For transformation from work-hardened
austenite (ε =0.5) T S decreases by 65°C when increasing the cooling rate from 1 to 78°C/s whereas
for accelerated cooling conditions (~60°C/s) T S increases by 40°C when the retained strain is
increased from 0 to 0.5.
Figure 1 − Effect of retained strain, ε , and cooling rate on the final microstructure resulting from an
austenite microstructure with d γ =14µm.
εεεε = 0 εεεε = 0.5
a 1oC/s
20 µµµµm
d) 88oC/s
20 µµµµm
c 60oC/s
20 µµµµm
b) 1oC/s
20 µµµµm
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Cooling Rate,oC/s
0 20 40 60 80 100
F e r r i t e G r a i n S i
z e , µ m
1
2
3
4
5ε=0ε=0.25ε=0.5
Figure 2 − Ferrite grain size as a function of cooling rate for an austenite grain size of 14µm andvarious levels of retained strain.
Model
In order to describe the austenite decomposition during continuous cooling a sequential
transformation model is proposed similar to that previously developed for other HSLA steels. This
approach consists of sub-models which predict the transformation start temperature, ferrite growth
kinetics and ferrite grain size. The effect of retained strain, ε , on the austenite decomposition was
incorporated in the model by means of an effective austenite grain size defined as follows [9],
)exp( ε γ −= d d eff (1)
The transformation start temperature, T S , is predicted with a model that combines corner
nucleation of ferrite with early growth, which was originally proposed for plain carbon steels [10].
The model assumes that early growth of corner ferrite nucleated at T N is controlled by carbon
diffusion in austenite. The radius of the growing ferrite grain, R f , can be calculated by [10],
f
o
c
f
Rcc
cc D
dt
dT
dT
dR 1
α γ
γ
−
−= (2)
assuming steady-state growth conditions along the grain boundaries where Dc is the diffusivity of
carbon in austenite, co is the average carbon concentration and cγ and cα are the equilibrium carbon
concentrations in austenite and ferrite, respectively. Orthoequilibrium is assumed in the
transformation start model and the required thermodynamic data are obtained from Thermo-Calc.
Nucleation site saturation at the austenite grain boundaries is achieved when the carbon enrichment
at the austenite grain boundaries reaches a critical level, c*, above which ferrite nucleation is
inhibited. This can be written as follows,
2
*eff
o
o
f
d
cc
cc R
−
−≥
γ
(3)
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and is suggested to coincide with measurable transformation start. Using equations (2) and (3) T S
can be predicted for any cooling path. For the present steel the model parameter T N was estimated
to be 787oC from the experimentally observed transformation start at a cooling rate of 1
oC/s and
d γ =14µm. The second model parameter c* can be represented as follows,
( ) o N cT T c ))0002.0exp(5.25.2(* 7.1−−+= (4)
Model predictions and observed transformation start temperatures for various strain levels and
austenite grain sizes are shown in Figure 3. The experimental T S is defined as the temperature
where 5% fraction transformed is observed. As seen in Figure 3, the proposed model provides an
accurate description of the observed transformation start temperature for the investigated cooling
conditions and initial austenite microstructures.
ϕdeff
2,
oCs
-1µm
2
101 102 103 104 105
U n d e r c o o l i n g ( A
e 3 - T s ) ,
o C
0
50
100
150
200
250
300
14 µm32 µm53 µm
ε 0 0.25 0.5
Model
Figure 3 – Undercooling for transformation start as a function of cooling rate , ϕ , and effective
austenite grain size, d eff .
The subsequent ferrite growth is modeled by employing the Johnson-Mehl-Avrami-Kolmogorov
(JMAK) approach, which is currently one of the most widely used transformation models in run-
out table process models [4], and adopting the additivity rule. In order to model the ferrite growth,
any non-polygonal and secondary transformation products and the associated kinetics were
excluded from the analysis. Thus, the analysis was applied to transformation kinetics that had a
minimum polygonal ferrite fraction of 85%, as determined from microstructural observations. Inthis approach, the normalized polygonal ferrite fraction transformed, X=Y/F eq, is introduced where
Y is the total fraction transformed and F eq is the orthoequilibrium polygonal ferrite fraction at each
temperature increment. In the JMAK model the change of X can be represented with respect to
time as follows,
[ ] nn
n X X nbdt
dX 11
)1ln()1(−
−−−= (5)
where the criterion for additivity is satisfied if the parameter b is a function of temperature and the
Avrami exponent, n, is a constant for any given initial austenite microstructure. The analysis of thepresent experimental data suggests that n=0.85 can be taken independent of the initial austenite
microstructure such that b is a function of temperature and initial austenite microstructure. For run-
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out table cooling conditions, b can be expressed as a function of undercooling below the Ae3
temperature and the initial effective austenite grain size in the format as previously proposed [4],
i.e.,
( )( )meff
Ae
d
bT T bb 231exp +−= (6)
where b1 , b2 and m are constants. For the present steel, m=2.2, b1=0.04K-1
and b2=−29.7 have been
determined. As shown in Figure 4 the proposed JMAK model provides an adequate description of
the ferrite formation during continuous cooling.
Temperature,oC
540 560 580 600 620 640 660 680
F e r r i t e F r a c t i o n
0.0
0.2
0.4
0.6
0.8
1.0
dγ = 14µm; ε = 0
dγ = 14µm; ε = 0.5
Model
dγ = 32µm; ε = 0
Figure 4 − Application of the JMAK model incorporating the effective austenite grain size for
various strain conditions and austenite grain sizes at a cooling rate of 25oC/s.
The ferrite grain size, d α , is essentially determined at the start of transformation assuming
nucleation site saturation and can be expressed as a function of the transformation start
temperature, i.e. [11],
3 / 1)]exp([ S T E BF d −=α (7)
where F is the final ferrite fraction, E is a constant, B depends on the initial austenitemicrostructure and T S is in Kelvin. The model parameter B can be written as a function of retained
strain and austenite grain size as follows,
( ) βε γ −+= exp Dd C B (8)
where C , D and β are model parameters. Quantifying d α as equivalent area diameter in µm,
C =13.4, D =0.056 µm-1
, β =6.3 and E =10000 K-1
have been found for the present steel where F is
approximated to be 0.9 from microstructural measurements. The model accurately describes the
ferrite grain size for the various strain conditions investigated as illustrated in Figure 5.
For sufficiently large values of ε the second term in equation (8) can be neglected and B becomes a constant, i.e. here B=13.4. Within the experimental error of the grain size measurements
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this convergence is attained for the highest strain level employed in the tests, i.e. ε =0.5. This
observation is similar to that made for other microalloyed low-carbon steels with similar yield
strength levels of 550MPa and higher [4][12]. As discussed by Nakata and Militzer [12] the ferrite
grain size obtained from sufficiently work-hardened austenite in these previously studied steels can
be presented as a function of transformation start temperature using equation (7) with steel
independent parameters, i.e. F =0.95, B=22.3 and E =18100. Even though these parameters aredifferent from those obtained for the present steel it is worthwhile to compare the predicted ferrite
grain sizes for both cases. This comparison is given in Figure 6 where the data of the 780MPa steel
studied in [12] are used to illustrate the behaviour of the previously investigated steels. As can be
seen, the predictions are similar in the fine-grained range which is associated with transformation
start temperatures of 600-650°C. However, for higher transformation start temperatures, the ferrite
grain size increases less rapidly in the present Mo-bearing steel than in those previously
investigated which do not contain Mo. Further studies are required to rationalize this finding.
Transformation Start Temperature,oC
620 640 660 680 700 720 740 760
F e r r i t e G r a i n S i z e , µ m
2.0
2.5
3.0
3.5
4.0
4.5
Model
ε 0 0.25 0.5
Figure 5 – Ferrite grain size as a function of transformation start temperature for d γ =32µm.
Transformation Start Temperature,oC
600 650 700 750 800
F e r r i t e G r a i n S i z
e , µ m
1
2
3
4
5 Present steel780 MPa steel [12]
Figure 6 − Ferrite grain sizes obtained from work-hardened austenite (ε =0.5) in the present steel
and a previously studied 780MPa HSLA steel [12]; lines indicate model predictions.
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Conclusions
The effects of cooling rate and initial austenite microstructure on austenite decomposition and
ferrite grain refinement have been quantified for a microalloyed low-carbon steel of 620MPa
minimum yield stress. Ferrite grain refinement from 4 to 2.1µm can be achieved with a
combination of accelerated cooling and deformation of austenite under no-recrystallization
condition, as observed by increasing the cooling rate from 1 of 88oC/s and the retained strain from
0 to 0.5 for d γ =14µm. Similar trends for ferrite refinement were observed for larger austenite grain
sizes. A previously proposed transformation model, with steel specific parameters, has been
applied which provides an accurate description for predicting the transformation start temperature,
ferrite growth and resulting ferrite grain size under run-out table cooling conditions for the
investigated steel. The fine ferrite grain sizes of approximately 2µm are associated with
transformation start temperatures in the range of 600-650°C which is similar to observations made
in other microalloyed steels of comparable strength levels.
Acknowledgments
Financial support received from the Natural Sciences and Engineering Research Council of Canada
(NSERC) is gratefully acknowledged. Materials were supplied by IPSCO Inc.
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Microalloying for New Steel Processes and Applications354