Fatigue & Fracture of
Engineering Materials & Structures
doi: 10.1111/j.1460-2695.2008.01318.x
Impact and tensile properties of ferrite–martensite dual-phase steels
T . D A L A L L I I S F A H A N I 1, A . S H A F Y E I 2 a n d H . S H A R I F I 1
1 Department
2 Department
of Materials and Metallurgical Engineering, Iran University of Science and Technology, Narmak, Tehran 16846-13114, Iran
of Materials Engineering, Isfahan University of Technology, Iran
Received in final form 4 December 2008
A B S T R A C T The effect of martensite morphology on the impact and tensile properties of dual phase
steels with a 0.25 volume fraction of martensite (V m ) under different heat treatments
was investigated. These treatments are direct quenching (DQ) and step quenching (SQ)
that result in different microstructures and mechanical properties. To process dual phase
steels, a low carbon manganese steel was used. At first the banding present in the initial
steel was eliminated, then the two different heat treatments were applied. To reach a
0.25 volume fraction of martensite a variation of intercritical annealing temperatures was
adopted for both treatments that allowed the evolution of different volume fraction of
martensite. Phase analysis showed that an intercritical temperature of 725 ◦ C (between
A 3 , A 1 ) gives the desired 0.25 V m of martensite. A comparison of impact, tensile and
ductile–brittle transition temperature (DBTT) indicates that the microstructure of the
direct treatment has a better toughness. The DBTT for the DQ and SQ treatment is −49
and −6 ◦ C, respectively.
Keywords dual phase steels; fixed volume fraction of martensite; impact properties;
toughness.
INTRODUCTION
Dual phase steels are classed as high strength low alloy
(HSLA) steels. These steels are developed from conventional low alloy steel, and their microstructure is
composed of relatively hard martensite particles which
imparts high strength dispersed in a relatively soft and
ductile ferrite matrix1,2 which supplies good elongation
that can produce a desirable combination of strength and
ductility.3–6 They are generally produced by an intercritical annealing in the austenite and ferrite region followed by a rapid cooling to ensure the transformation of
the austenite to the martensite.7,8 In addition to the two
phases present in this composite microstructure, depending on cooling rate, it may also contain retained austenite,
new ferrite (epitaxial ferrite) and bainite.9–11
In recent years, application of high strength steels, especially dual phase steels, have made a great improvement
in the automotive industry. This improvement originates
from the characteristics of dual phase steels. By this, we
mean the combination of high strength, good ductility,
good weldability, low yield stress to tensile strength ratio (YS/TS), continuous yielding and high initial workhardening rates (n values). Also, due to its high strength,
Correspondence: T. Dalalli Isfahani. E-mail: tdi1359@iust.ac.ir
c 2009 Blackwell Publishing Ltd. Fatigue Fract Engng Mater Struct 32, 141–147
a thinner plate can be used for a specific strength in contrast with usual steels, which results in weight saving of
products.12,13
In the production of dual phase steels, different heat
treatment procedures (or quenching paths) can be applied
which result in different microstructures and mechanical
properties due to the different morphology of martensite.
Resulting microstructures consist of ferrite and martensite phases, but the volume fraction and morphology are
largely varied by the quenching paths. Among the different procedures the direct (or intercritical) quenching
and step quenching are mostly used in industry. The
martensite in direct and step quenched specimens has
the morphology of spherical and network martensite
for the former, and aggregates of large, blocky shaped
martensite islands for the latter.14–17 Using dual phase
steels with a 0.25 volume fraction of martensite makes the
best combination of the useful properties in the automotive industry.18–20
Some of the factors that influence the impact properties are morphology, distribution and carbon content of
martensite phase as well as the grain size.21–24
Previous studies have mainly focused on high-martensite
dual phase steels which are not appropriate for use in automotive industry because of their low ductility and toughness properties. The previous work, on low-martensite
141
142
T . D A L A L L I I S F A H A N I et al.
Table 1 Composition of the steel used
Steel
C-Mn
Composition (wt%)
Fe
C
P
S
Si
Mn
Cr
Mo
Ni
97.84
0.137
0.028
0.022
0.30
1.57
0.02
0.01>
<0.02
Al
0.03
Co
<0.02
Cu
0.01
Nb
0.02
Ti
<0.01
V
<0.01
W
<0.04
Zr
<0.003
Pb
<0.01
dual phase steels were mainly involved with fatigue properties, but in this research the impact properties are discussed, using the obtained Charpy curves. From these
curves the ductile–brittle transition temperature (DBTT)
are identified.
As mentioned previously the purpose of the current
study was to obtain the impact and tensile properties of
dual phase steels with 0.25 V m martensite, different morphology and distribution of martensite with a fixed grain
size.
In this paper the DBTT for the different microstructures
of dual phase steels with 0.25 V m is also presented.
for 4 h (cooled in the furnace), then normalized at
910 ◦ C for 20 min. to make fine pearlite instead of the
coarse ones which resulted in a smaller grain size. The
austenitizing temperatures Ac 1 and Ac 3 , which define
the ferrite and austenite region were calculated by using
Eqs (1) and (2) with temperature degrees of 715 and
820 ◦ C, respectively.
Ac1 = 723 − 10.7Mn − 16.9Ni + 29.1Si + 16.9Cr
+ 290As + 6.38W
√
Ac3 = 910 − 203 C − 15.2Ni + 44.7Si
+ 104V + 31.5Mo + 13.1W
EXPERIMENTAL PROCEDURE
The composition of the steel used is shown in Table 1. It
was supplied in the form of hot rolled plate with 10 mm
thickness that had a ferrite-pearlite structure with slight
banding (Fig. 1).
To eliminate the banding present in the initial steel at the
first stage, the specimens were homogenized at 1200 ◦ C
(1)
(2)
The intercritical thermal treatments were performed
at 715, 725,750,775 and 800 ◦ C for 1 h, followed by
quenching in brine solution. After etching by nital 3%
the microstructure was analysed with the help of an optical microscope and utilization of image analysis software
for determination of volume fraction and grain sizes. In
each sample, image analysis was carried out in at least ten
Fig. 1 Banding present in the
ferrite-pearlite microstructure of the initial
steel.
c 2009 Blackwell Publishing Ltd. Fatigue Fract Engng Mater Struct 32, 141–147
IMPACT AND TENSILE PROPERTIES OF FERRITE–MARTENSITE DUAL-PHASE STEELS
143
Fig. 2 Microstructure of dual phase steel
achieved from direct quenching ×750 (a)
and step quenching ×750 (b).
different regions of the specimen. The analysing experiment showed that the 0.25 volume fraction of martensite
was obtained with the use of intercritical temperature at
725 ◦ C .This temperature was the same for both, the direct quenching (DQ) and the step quenching (SQ) heat
treatment schedules. The two different microstructures
obtained are shown in Fig. 2.
As mentioned before, in order to achieve different
microstructures two different procedures were applied.
The first procedure involved an intercritical treatment at
725 ◦ C for 60 min, followed by quenching in brine solution, and the second procedure involved austenitizing
c 2009 Blackwell Publishing Ltd. Fatigue Fract Engng Mater Struct 32, 141–147
at 910 ◦ C for 20 min, followed by furnace cooling to the
required intercritical temperature of 725 ◦ C for a 60 min
duration before quenching in brine solution. The former
has spherical and network morphology while the latter
contains aggregates of large, blocky shaped martensite islands. The heat treatment procedures used to achieve different morphologies of martensite from the initial steel
are schematically presented in Figs 3 and 4.
To make sure that the two phases present in the microstructure are ferrite and martensite, microhardness
was applied. At least six hardness values were taken in
each sample. The soft phase had a hardness value around
144
T . D A L A L L I I S F A H A N I et al.
250
Initial Steel
200
Energy (Joule)
Direct quenched
150
100
Step quenched
50
Fig. 3 Heat treatment used to achieve a dual phase structure from
the initial steel using direct quenching.
0
-100
-50
0
50
100
-50
Temperature (°C)
Fig. 6 Comparison of charpy curves for the two different dual
phase steels and the initial steel (homogenized and normalized).
Fig. 4 Heat treatment used to achieve a dual phase structure from
the initial steel using step quenching.
1000
900
Step quenched
Stress (Mpa)
800
700
Direct quenched
phase steels. On the other hand the initial steel has a noncontinuous yielding which is characterized by the luder
bands.
Impact testing of the V notch specimens was carried out,
after which the charpy curves were plotted for initial, direct quenched and step quenched specimens. The charpy
curves for the two different microstructures of the dual
phase steels and the homogenized and austenized initial
steel are shown in Fig. 6. Fracture surfaces of impact specimens were analysed using a scanning electron microscope
(Figs 7 and 8).
600
500
RESULTS AND DISCUSSION
400
300
Initial Steel
200
100
0
0
20
40
60
Strain
Fig. 5 Comparison between the two different dual phase steels and
the initial steel (homogenized and normalized).
200 Vickers while the harder phase had a value around
510 Vickers which proves that we have obtained a ferrite–
martensite microstructure. Tensile testing of the specimens, in accordance with ASTM standard (A370-B),
was conducted at room temperature in a computer controlled Housfield machine using a cross head velocity of
0.50 mm/min. The true stress–true strain curves of the
dual phase steels obtained by step and direct quenching
and also for the homogenized and austenitized initial steel
are shown in Fig. 5. As shown the step quenched and direct quenched specimens have continuous yielding which
is the unique characterization of ferrite–martensite dual
The two morphologies obtained from different heat treatment procedures result in varying mechanical properties.
From the true stress–true strain curves (Fig. 5) it can be
seen that both of the dual phase steels have better tensile
properties than the initial homogenized and normalized
steel. The basic reason is that pearlite is substituted by
martensite which is a harder phase. Martensite acts like
a reinforcement in the dual phase steel. As well as this,
the dual phase microstructures have continuous yielding
which is a unique property of the dual phase steels due to
their composite microstructure. This results in desirable
formed surfaces but the initial steel has non-continuous
yielding resulting in bad formed surfaces. The dual phase
steel obtained by the step quenching procedure has a
better tensile property than the direct quenching procedure. As mentioned by others25,26 due to the 3–4 volume
percent expansion forced by the austenite to martensite
transformation the dislocation concentration around
the brittle martensite phase is high which causes the ferrite
phase to be under stress. In the direct quenched specimens
we have a uniform distribution of small spherical, network
martensite resulting in a more uniform distribution of dislocations. This results in less concentration of dislocation
c 2009 Blackwell Publishing Ltd. Fatigue Fract Engng Mater Struct 32, 141–147
IMPACT AND TENSILE PROPERTIES OF FERRITE–MARTENSITE DUAL-PHASE STEELS
145
Fig. 7 Fracture surfaces of the dual phase
steel obtained from direct (a) and step
quenched (b) specimens above the DBTT
temperatures showing a ductile fracture.
so the locking of dislocations is less. However, in the
step quenched specimens we have large blocky martensite islands, which results in a non-uniform distribution
of martensite and also the concentration of martensite in
different parts of the specimen due to the less uniformity
compared to the spherical and network morphology of
the direct quenched specimen which originates from the
larger size of the blocky martensite islands. This concentration causes more locked dislocations that result in a
higher tensile property. The curves in Fig. 5 indicate that
work hardening as a result of locked dislocations is higher
in the step quenched specimen than the direct quenched
specimen. From all the mentioned reasons and as shown
c 2009 Blackwell Publishing Ltd. Fatigue Fract Engng Mater Struct 32, 141–147
by the curve we can mention that more elongation and a
better formability are possible by direct quenched specimens. High work hardening rate and low yield stress to
tensile strength ratio ( YTSS ) of steels are other important
characteristics of dual phase steels making them suitable
for many industries such as automobile industry. The ( YTSS )
ratio for the step quenched specimen, direct quenched
specimen and the initial steel is 0.54, 0.55 and 0.676,
respectively. The other tensile properties are given in
Table 2.
From the Charpy curves plotted with the data’s obtained
by the impact test we see that the DBTT for the direct
quenched, step quenched and initial steel are −49, −6 and
146
T . D A L A L L I I S F A H A N I et al.
Fig. 8 Fracture surfaces of the dual phase
steel obtained from direct (a) and step
quenched (b) specimens under the DBTT
temperatures showing a brittle fracture.
Table 2 Tensile properties
Initial Steel
Direct quenched
Step quenched
YS (Mpa)
UTS (Mpa)
( YTSS )
359
406
523
531
751
950
0.676
0.540
0.550
−34 ◦ C, respectively. We can see that the impact property
of the direct quenched specimen has improved from the
initial steel but the step quenched specimen has become
worse. The reason is that in the step quenched specimen
we have a large number of locked dislocations which cause
low ductility. Also in low temperatures the mobility of dislocation are low which causes more locked dislocations in
different parts of high concentrated martensite. All these
reasons cause lower impact energy and impact strength.
In the direct quenched specimen we have more ductility resulting in better impact property. It can also be seen
that the impact strength of the initial and direct quenched
steel is greater while the step quenched specimen has a low
value.
The martensite phase in the step quenched specimen
is located at some parts of the grain boundary in a noncontinuous way that results in poor impact property. SEM
of fractured surfaces (Figs 7 and 8) above and beneath the
c 2009 Blackwell Publishing Ltd. Fatigue Fract Engng Mater Struct 32, 141–147
IMPACT AND TENSILE PROPERTIES OF FERRITE–MARTENSITE DUAL-PHASE STEELS
DBTT for both step quenched and direct quenched dual
phase steels are shown (the micrographs were taken from
the fracture surfaces of impact specimens). In the case of
ductile fracture we see dimples and in the brittle case we
have cleavage fracture. From the SEM of fractured surfaces above the DBTT it can be seen that in Fig. 7a we
have only dimples but in Fig. 7b, some parts with cleavage
fracture are seen along with dimples which indicates that
the step quenched specimens have a more brittle property.
Also, Fig. 7a has smaller dimples and a more uniform distribution compared to Fig. 7b. As shown in Fig. 8b we
have only cleavage fracture while in the direct quenched
specimen (Fig. 8a), both dimples and cleavage parts can
be seen. Also, it can be seen from Fig. 8b that we have big
cleavage parts and the cleavage parts are not uniformly
distributed and are concentrated in different parts of the
microstructure. This is probably due to the presence of
large blocky martensite islands. Figures 7a and 8a are referred to direct quenched and Figs 7b and 8b are referred
to step quenched specimens.
CONCLUSION
As Fig. 5 shows we can conclude that tensile properties
for both of the dual phase steels are desirable, the dual
phase steel obtained from step quenching has a better
tensile strength while the direct quenched specimen has
a better ductility. As Fig. 6 represents we understand that
the specimen prepared with the use of step quenching
has such a bad impact property that makes the use of this
microstructure impossible.
On the other hand using direct quenching improves the
impact property while step quenching deteriorates it. The
DBTT for direct quenching, step quenching and the initial steel (homogenized and normalized) are −49, −6 and
−34, respectively.
Overall, we can conclude that using dual phase steels
obtained from direct quenching for those products that
need a combination of impact and tensile properties is
desirable.
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Acknowledgements
The authors are grateful to Mr. Hamid Ghayour and Mr.
Mostafa Mirjalili for advice in preparing the paper.
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