TECHNICAL FIELD
[0001] The present invention relates to a high-carbon steel sheet with improved formability
and a method of manufacturing the same.
BACKGROUND ART
[0002] A high-carbon steel sheet is used for various steel products, which are a driving
system component for automobile such as a chain, a gear and a clutch, a saw, a knife,
and others. When the steel products are manufactured, forming and heat treatments
of a high-carbon steel sheet are performed. As the forming, punching, tensile forming,
compressing, shearing, and so on are performed, and as the heat treatment, quenching,
tempering, carburizing, nitriding, soft-nitriding, and so on are performed. A strength
of a high-carbon steel sheet is higher than that of a mild steel sheet, and therefore
a metal mold used for forming of a high-carbon steel sheet is more easily worn than
a metal mold used for forming of a mild steel sheet. Further, a high-carbon steel
sheet cracks more easily than a mild steel sheet during forming.
[0003] For suppressing the wearing of a metal mold, improving lubricity on a surface of
a high-carbon steel sheet is effective, and for suppressing the cracking during forming,
softening of a high-carbon steel sheet is effective. Thus, some techniques have been
proposed aiming at an improvement in lubricity and softening (Patent Literatures 1
to 5).
[0004] However, these prior techniques cause a significant increase in cost, and therefore
are not preferred.
[0005] Although a carbon steel sheet aiming at an improvement in punchability has been described
in Patent Literature 6 and a high-carbon steel sheet aiming at an improvement in formability
has been described in Patent Literature 7, it is not possible for them to obtain sufficient
formability. Other previously proposed arrangements are disclosed in
JP2011208164A.
CITATION LIST
PATENT LITERATURE
[0006]
Patent Literature 1: Japanese Laid-open Patent Publication No. 2010-174252
Patent Literature 2: Japanese Laid-open Patent Publication No. 2009-215612
Patent Literature 3: Japanese Laid-open Patent Publication No. 2011-168842
Patent Literature 4: Japanese Laid-open Patent Publication No. 2010-255066
Patent Literature 5: Japanese Laid-open Patent Publication No. 2000-34542
Patent Literature 6: Japanese Laid-open Patent Publication No. 2000-265240
Patent Literature 7: Japanese Laid-open Patent Publication No. 10-147816
SUMMARY OF INVENTION
TECHNICAL PROBLEM
[0007] An object of the present invention is to provide a high-carbon steel sheet capable
of obtaining excellent formability while avoiding a significant increase in cost,
and a method of manufacturing the same.
SOLUTION TO PROBLEM
[0008] The present inventors conducted earnest studies repeatedly to solve the above-described
problem, and consequently found out that it is important that a high-carbon steel
sheet contains a specific amount of B, that a coefficient of micro-friction of ferrite
on a surface is a specific one, and that form of cementite is a specific one. Further,
it was also found out that, in order to manufacture such a high-carbon steel sheet,
it is important to perform hot-rolling and annealing under specific conditions while
assuming hot-rolling and annealing as what is called a consecutive process. Then,
the inventors of the present application devised the following various aspects of
the invention based on these findings.
- (1) A high-carbon steel sheet, including:
a chemical composition represented by, in mass%:
C: 0.30% to 0.70%,
Si: 0.07% to 1.00%,
Mn: 0.20% to 3.00%,
Ti: 0.010% to 0.500%,
Cr: 0.01% to 1.50%,
B: 0.0004% to 0.0035%,
P: 0.025% or less,
Al: 0.100% or less,
S: 0.0100% or less,
N: 0.010% or less,
Cu: 0.500% or less,
Nb: 0.000% to 0.500%,
Mo: 0.000% to 0.500%,
V: 0.000% to 0.500%,
W: 0.000% to 0.500%,
Ta: 0.000% to 0.500%,
Ni: 0.000% to 0.500%,
Mg: 0.000% to 0.500%,
Ca: 0.000% to 0.500%,
Y: 0.000% to 0.500%,
Zr: 0.000% to 0.500%,
La: 0.000% to 0.500%,
Ce: 0.000% to 0.500%, and
balance: Fe and impurities; and
a structure represented by:
a spheroidized ratio of cementite: 80% or more; and
an average diameter of cementite: 0.3 µm to 2.2 µm, wherein
a coefficient of micro-friction of ferrite on a surface of the steel sheet is less
than 0.5.
- (2) The high-carbon steel sheet according to (1), wherein
in the chemical composition,
Nb: 0.001% to 0.500%,
Mo: 0.001% to 0.500%,
V: 0.001% to 0.500%,
W: 0.001% to 0.500%,
Ta: 0.001% to 0.500%,
Ni: 0.001% to 0.500%,
Mg: 0.001% to 0.500%,
Ca: 0.001% to 0.500%,
Y: 0.001% to 0.500%,
Zr: 0.001% to 0.500%,
La: 0.001% to 0.500%, or
Ce: 0.001% to 0.500%, or
any combination thereof is satisfied.
- (3) A method of manufacturing a high-carbon steel sheet, including:
hot-rolling of a slab so as to obtain a hot-rolled steel sheet;
pickling of the hot-rolled steel sheet; and
annealing of the hot-rolled steel sheet after the pickling,
the slab including a chemical composition represented by, in mass%:
C: 0.30% to 0.70%,
Si: 0.07% to 1.00%,
Mn: 0.20% to 3.00%,
Ti: 0.010% to 0.500%,
Cr: 0.01% to 1.50%,
B: 0.0004% to 0.0035%,
P: 0.025% or less,
Al: 0.100% or less,
S: 0.0100% or less,
N: 0.010% or less,
Cu: 0.500% or less,
Nb: 0.000% to 0.500%,
Mo: 0.000% to 0.500%,
V: 0.000% to 0.500%,
W: 0.000% to 0.500%,
Ta: 0.000% to 0.500%,
Ni: 0.000% to 0.500%,
Mg: 0.000% to 0.500%,
Ca: 0.000% to 0.500%,
Y: 0.000% to 0.500%,
Zr: 0.000% to 0.500%,
La: 0.000% to 0.500%,
Ce: 0.000% to 0.500%, and
balance: Fe and impurities, wherein
in the hot-rolling,
the slab is heated at a temperature of 1000°C or more and less than 1150°C,
a finish rolling temperature is 830°C or more and 950°C or less, and
a coiling temperature is 450°C or more and 700°C or less, and
the annealing comprises:
retaining the hot-rolled steel sheet at a temperature of 730°C or more and 770°C or
less for 3 hours or more and 60 hours or less; and
then cooling the hot-rolled steel sheet down to 650°C at a cooling rate of 1°C/hr
or more and 60°C/hr or less.
- (4) The method of manufacturing the high-carbon steel sheet according to (3), wherein
in the chemical composition,
Nb: 0.001% to 0.500%,
Mo: 0.001% to 0.500%,
V: 0.001% to 0.500%,
W: 0.001% to 0.500%,
Ta: 0.001% to 0.500%,
Ni: 0.001% to 0.500%,
Mg: 0.001% to 0.500%,
Ca: 0.001% to 0.500%,
Y: 0.001% to 0.500%,
Zr: 0.001% to 0.500%,
La: 0.001% to 0.500%, or
Ce: 0.001% to 0.500%, or
any combination thereof is satisfied.
ADVANTAGEOUS EFFECTS OF INVENTION
[0009] According to the present invention, a B content, a coefficient of micro-friction
of ferrite on a surface and others are appropriate, thereby making it possible to
obtain excellent formability while avoiding a significant increase in cost.
BRIEF DESCRIPTION OF DRAWINGS
[0010]
[Fig. 1] Fig. 1 is a chart illustrating a relationship between a coefficient of micro-friction
of ferrite and a B content;
[Fig. 2] Fig. 2 is a chart illustrating a relationship between a coefficient of micro-friction
of ferrite and a number of pressing until a flaw occurs;
[Fig. 3A] Fig. 3A is a micrograph showing a surface of a high-carbon steel sheet before
measuring a coefficient of micro-friction;
[Fig. 3B] Fig. 3B is a micrograph showing the surface of the high-carbon steel sheet
after measuring the coefficient of micro-friction;
[Fig. 4] Fig. 4 is a schematic diagram illustrating changes in temperature from hot-rolling
to cooling;
[Fig. 5A] Fig. 5A is a schematic diagram illustrating a structure at time tA;
[Fig. 5B] Fig. 5B is a schematic diagram illustrating a structure at time tB;
[Fig. 5C] Fig. 5C is a schematic diagram illustrating a structure at time tC;
[Fig. 5D] Fig. 5D is a schematic diagram illustrating a structure at time tD;
[Fig. 5E] Fig. 5E is a schematic diagram illustrating a structure at time tE;
[Fig. 6A] Fig. 6A is a schematic diagram illustrating a structure when a slab heating
temperature is high than 1150°C;
[Fig. 6B] Fig. 6B is a schematic diagram illustrating a structure when the slab heating
temperature is lower than 1000°C;
[Fig. 6C] Fig. 6C is a schematic diagram illustrating a structure when an annealing
retention temperature is lower than 730°C;
[Fig. 6D] Fig. 6D is a schematic diagram illustrating a structure when the annealing
retention temperature is higher than 770°C or an annealing retention is longer than
60 hours;
[Fig. 6E] Fig. 6E is a schematic diagram illustrating a structure when the annealing
retention is shorter than 3 hours;
[Fig. 6F] Fig. 6F is a schematic diagram illustrating a structure when a cooling rate
is less than 1°C/hr;
[Fig. 6G] Fig. 6G is a schematic diagram illustrating a structure when the cooling
rate is greater than 60°C/hr; and
[Fig. 7] Fig. 7 is a chart illustrating a relationship between a coefficient of micro-friction
of ferrite and a B content for a part of inventive examples in a first experiment
or a third experiment.
DESCRIPTION OF EMBODIMENTS
[0011] Hereinafter, there will be explained an embodiment of the present invention.
[0012] First, chemical compositions of a high-carbon steel sheet according to the embodiment
of the present invention and a slab (steel ingot) used for manufacturing the same
will be explained. Although details will be described later, the high-carbon steel
sheet according to the embodiment of the present invention is manufactured by going
through hot-rolling of the slab, annealing, and the like. Accordingly, the chemical
compositions of the high-carbon steel sheet and the slab are appropriate for the above-stated
processes in addition to properties of the high-carbon steel sheet. In the following
description, "%" being a unit of content of each element contained in the high-carbon
steel sheet and the slab used for manufacturing the same means "mass%" unless otherwise
mentioned. The high-carbon steel sheet according to the embodiment and the slab used
for manufacturing the same include a chemical composition represented by C: 0.30%
to 0.70%, Si: 0.07% to 1.00%, Mn: 0.20% to 3.00%, Ti: 0.010% to 0.500%, Cr: 0.01%
to 1.50%, B: 0.0004% to 0.0035%, P: 0.025% or less, Al: 0.100% or less, S: 0.0100%
or less, N: 0.010% or less, Cu: 0.500% or less, Nb: 0.000% to 0.500%, Mo: 0.000% to
0.500%, V: 0.000% to 0.500%, W: 0.000% to 0.500%, Ta: 0.000% to 0.500%, Ni: 0.000%
to 0.500%, Mg: 0.000% to 0.500%, Ca: 0.000% to 0.500%, Y: 0.000% to 0.500%, Zr: 0.000%
to 0.500%, La: 0.000% to 0.500%, Ce: 0.000% to 0.500%, and balance: Fe and impurities.
As the impurities, ones contained in raw materials such as ore and scrap, and ones
contained during a manufacturing process are exemplified. For example, when scrap
is used as a raw material, Sn, Sb or As or any combination thereof may mix in by 0.003%
or more. If the content is 0.03% or less, none of them hinder the effect of the embodiment,
and thus may be tolerated as impurities. Further, O may be tolerated as an impurity
up to 0.0025%. O forms oxide, and when oxides aggregate and become coarse, sufficient
formability is not obtained. Therefore, the O content is the lower the better. However,
it is technically difficult to decrease the O content to less than 0.0001%.
(C: 0.30% to 0.70%)
[0013] C bonds to Fe to form cementite having a small friction coefficient, and thus is
an important element when securing macro-lubricity of the high-carbon steel sheet.
When the C content is less than 0.30%, the amount of cementite is insufficient, resulting
in that sufficient lubricity cannot be obtained and adhesion to a metal mold occurs
during forming. Thus, the C content is 0.30% or more, and preferably 0.35% or more.
When the C content is greater than 0.70%, the amount of cementite is excessive, resulting
in that a crack originating from the cementite occurs easily during forming. Thus,
the C content is 0.70% or less, and preferably 0.65% or less.
(Si: 0.07% to 1.00%)
[0014] Si operates as a deoxidizer, and is effective for suppressing excessive coarsening
of cementite during annealing. When the Si content is less than 0.07%, the effect
by the above-described operation cannot be obtained sufficiently. Thus, the Si content
is 0.07% or more, and preferably 0.10% or more. When the Si content is greater than
1.00%, the ductility of ferrite is low and a crack originating from transgranular
fracture of ferrite occurs easily during forming. Thus, the Si content is 1.00% or
less, and preferably 0.80% or less.
(Mn: 0.20% to 3.00%)
[0015] Mn is important for controlling pearlite transformation. When the Mn content is less
than 0.20%, the effect by the above-described operation cannot be obtained sufficiently.
That is, when the Mn content is less than 0.20%, pearlite transformation occurs in
cooling after dual-phase annealing and a spheroidized ratio of cementite becomes insufficient.
Thus, the Mn content is 0.20% or more, and preferably 0.25% or more. When the Mn content
is greater than 3.00%, the ductility of ferrite is low and a crack originating from
transgranular fracture of ferrite occurs easily during forming. Thus, the Mn content
is 3.00% or less, and preferably 2.00% or less.
(Ti: 0.010% to 0.500%)
[0016] Ti forms a nitride in molten steel, and effective for preventing formation of BN.
When the Ti content is less than 0.010%, the effect by the above-described operation
cannot be obtained sufficiently. Thus the Ti content is 0,010% or more, and preferably
0.040% or more. When the Ti content is greater than 0.500%, a crack originating from
a coarse oxide of Ti occurs easily during forming. This is because during continuous
casting, coarse oxides of Ti are formed to get involved inside the slab. Thus, the
Ti content is 0.500% or less, and preferably 0.450% or less.
(Cr: 0.01% to 1.50%)
[0017] Cr has a high affinity with N, effective for suppressing formation of BN, and effective
also for controlling pearlite transformation. When the Cr content is less than 0.01%,
the effect by the above-described operation cannot be obtained sufficiently. Thus,
the Cr content is 0.01% or more, and preferably 0.05% or more. When the Cr content
is greater than 1.50%, spheroidizing of cementite during annealing is hindered and
coarsening of cementite is suppressed drastically. Thus, the Cr content is 1.50% or
less, and preferably 0.90% or less.
(B: 0.0004% to 0.0035%)
[0018] B lowers the coefficient of micro-friction of ferrite on the surface of the high-carbon
steel sheet. B segregates to and concentrates at an interface between ferrite and
cementite during later-described annealing and suppresses peeling at the interface
during forming, and B is also effective for preventing a crack. When the B content
is less than 0.0004%, the effect by the above-described operation cannot be obtained
sufficiently. Thus, the B content is 0.0004% or more, and preferably 0.0008% or more.
When the B content is greater than 0.0035%, a crack originating from boride such as
carbide of Fe and B occurs easily during forming. Thus, the B content is 0.0035% or
less, and preferably 0.0030% or less.
[0019] Fig. 1 is a chart illustrating a relationship between a coefficient of micro-friction
of ferrite and a B content. As illustrated in Fig. 1, when the B content is 0.0004%
or more, the coefficient of micro-friction of ferrite is significantly low as compared
to the case when it is less than 0.0004%. It may be inferred that the reason why wearing
of a metal mold can be suppressed as a coefficient of micro-friction of ferrite is
lower is because a hard film of B is formed on a surface of a high-carbon steel sheet,
as will be described later. Further, it may be inferred that the operation that B
segregated to and concentrated at an interface between ferrite and cementite improves
strength of the interface, suppresses cracking of a high-carbon steel sheet, and suppresses
wearing of a metal mold caused by cracking is also a reason for the above.
(P: 0.025% or less)
[0020] P is not an essential element and is contained as an impurity in the steel sheet,
for example. P strongly segregates to the interface between ferrite and cementite,
and thereby the segregation of B to the interface is hindered and peeling at the interface
is caused. Therefore, the P content is the smaller the better. When the P content
is greater than 0.025%, adverse effects are particularly prominent. Thus, the P content
is 0.025% or less. Decreasing the P content takes refining cost, and it requires a
considerable refining cost to decrease the P content to less than 0.0001%. Thus, the
P content may be 0.0001% or more.
(Al: 0.100% or less)
[0021] Al operates as a deoxidizer in steelmaking and is effective for fixing N, but is
not an essential element of the high-carbon steel sheet and is contained as an impurity
in the steel sheet, for example. When the Al content is greater than 0.100%, the ductility
of ferrite is low and a crack originating from transgranular fracture of ferrite occurs
easily during forming, and strength is excessive to cause an increase in forming load.
[0022] Thus, the Al content is set to 0.100% or less. When the Al content of the high-carbon
steel sheet is less than 0.001%, fixation of N sometimes may be insufficient. Thus,
the Al content may be 0.001% or more.
(S: 0.0100% or less)
[0023] S is not an essential element and is contained as an impurity in the steel sheet,
for example. S forms coarse non-metal inclusions such as MnS to impair formability.
Therefore, the S content is the smaller the better. When the S content is greater
than 0.0100%, adverse effects are particularly prominent. Thus, the S content is 0.0100%
or less. Decreasing the S content takes refining cost, and it requires a considerable
refining cost to decrease the S content to less than 0.0001%. Thus, the S content
may be 0.0001% or more.
(N: 0.010% or less)
[0024] N is not an essential element and is contained as an impurity in the steel sheet,
for example. N lowers an amount of solid-solution B due to formation of BN so as to
cause adhesion to the metal mold, cracking during forming, and the like. Therefore,
the N content is the smaller the better. When the N content is greater than 0.010%,
adverse effects are particularly prominent. Thus, the N content is set to 0.010% or
less. Decreasing the N content takes refining cost, and it requires a considerable
refining cost to decrease the N content to less than 0.001%. Thus, the N content may
be 0.001% or more.
(Cu: 0.000% to 0.500%)
[0025] Cu is not an essential element and is mixed from scrap or the like to be contained
as an impurity in the steel sheet, for example. Cu causes an increase in strength
and brittleness in hot working. Therefore, the Cu content is the smaller the better.
When the Cu content is greater than 0.500%, adverse effects are particularly prominent.
Thus, the Cu content is 0.500% or less. Decreasing the Cu content takes refining cost,
and it requires a considerable refining cost to decrease the Cu content to less than
0.001%. Thus, the Cu content may be 0.001% or more.
[0026] Nb, Mo, V, W, Ta, Ni, Mg, Ca, Y, Zr, La, and Ce are not essential elements, and are
optional elements that may be appropriately contained in the high-carbon steel sheet
and the slab up to a specific amount.
(Nb: 0.000% to 0.500%)
[0027] Nb forms a nitride and is effective for suppressing formation of BN. Thus, Nb may
be contained. However, when the Nb content is greater than 0.500%, the ductility of
ferrite is low to make it impossible to obtain sufficient formability.
[0028] Thus, the Nb content is 0.500% or less. In order to securely obtain the effect by
the above-described operation, the Nb content is preferably 0.001% or more.
(Mo: 0.000% to 0.500%)
[0029] Mo is effective for improving hardenability. Thus, Mo may be contained. However,
when the Mo content is greater than 0.500%, the ductility of ferrite is low to make
it impossible to obtain sufficient formability. Thus, the Mo content is 0.500% or
less. In order to securely obtain the effect by the above-described operation, the
Mo content is preferably 0.001% or more.
(V: 0.000% to 0.500%)
[0030] V forms a nitride and is effective for suppressing formation of BN similarly to Nb.
Thus, V may be contained. However, when the V content is greater than 0.500%, the
ductility of ferrite is low to make it impossible to obtain sufficient formability.
Thus, the V content is 0.500% or less. In order to securely obtain the effect by the
above-described operation, the V content is preferably 0.001% or more.
(W: 0.000% to 0.500%)
[0031] W is effective for improving hardenability similarly to Mo. Thus, W may be contained.
However, when the W content is greater than 0.500%, the ductility of ferrite is low
to make it impossible to obtain sufficient formability. Thus, the W content is 0.500%
or less. In order to securely obtain the effect by the above-described operation,
the W content is preferably 0.001% or more.
(Ta: 0.000% to 0.500%)
[0032] Ta forms a nitride and is effective for suppressing formation of BN similarly to
Nb and V. Thus, Ta may be contained. However, when the Ta content is greater than
0.500%, the ductility of ferrite is low to make it impossible to obtain sufficient
formability. Thus, the Ta content is 0.500% or less. In order to securely obtain the
effect by the above-described operation, the Ta content is preferably 0.001% or more.
(Ni: 0.000% to 0.500%)
[0033] Ni is effective for improving toughness and improving hardenability. Thus, Ni may
be contained. However, when the Ni content is greater than 0.500%, the coefficient
of micro-friction of ferrite is high to cause adhesion to the metal mold easily. Thus,
the Ni content is 0.500% or less. In order to securely obtain the effect by the above-described
operation, the Ni content is preferably 0.001% or more.
(Mg: 0.000% to 0.500%)
[0034] Mg is effective for controlling the form of sulfide. Thus, Mg may be contained. However,
Mg forms oxide easily, and when the Mg content is greater than 0.500%, sufficient
formability cannot be obtained due to a crack originating from the oxide. Thus, the
Mg content is 0.500% or less. In order to securely obtain the effect by the above-described
operation, the Mg content is preferably 0.001% or more.
(Ca: 0.000% to 0.500%)
[0035] Ca is effective for controlling the form of sulfide similarly to Mg. Thus, Ca may
be contained. However, Ca forms oxide easily, and when the Ca content is greater than
0.500%, sufficient formability cannot be obtained due to a crack originating from
the oxide. Thus, the Ca content is 0.500% or less. In order to securely obtain the
effect by the above-described operation, the Ca content is preferably 0.001% or more.
(Y: 0.000% to 0.500%)
[0036] Y is effective for controlling the form of sulfide similarly to Mg and Ca. Thus,
Y may be contained. However, Y forms oxide easily, and when the Y content is greater
than 0.500%, sufficient formability cannot be obtained due to a crack originating
from the oxide. Thus, the Y content is 0.500% or less. In order to securely obtain
the effect by the above-described operation, the Y content is preferably 0.001% or
more.
(Zr: 0.000% to 0.500%)
[0037] Zr is effective for controlling the form of sulfide similarly to Mg, Ca, and Y. Thus,
Zr may be contained. However, Zn forms oxide easily, and when the Zr content is greater
than 0.500%, sufficient formability cannot be obtained due to a crack originating
from the oxide. Thus, the Zr content is 0.500% or less. In order to securely obtain
the effect by the above-described operation, the Zr content is preferably 0.001% or
more.
(La: 0.000% to 0.500%)
[0038] La is effective for controlling the form of sulfide similarly to Mg, Ca, Y, and Zr.
Thus, La may be contained. However, La forms oxide easily, and when the La content
is greater than 0.500%, sufficient formability cannot be obtained due to a crack originating
from the oxide,. Thus, the La content is 0.500% or less. In order to securely obtain
the effect by the above-described operation, the La content is preferably 0.001% or
more.
(Ce: 0.000% to 0.500%)
[0039] Ce is effective for controlling the form of sulfide similarly to Mg, Ca, Y, Zr, and
La. Thus, Ce may be contained. However, Ce forms oxide easily, and when the Ce content
is greater than 0.500%, sufficient formability cannot be obtained due to a crack originating
from the oxide,. Thus, the Ce content is 0.500% or less. In order to securely obtain
the effect by the above-described operation, the Ce content is preferably 0.001% or
more.
[0040] Thus, Nb, Mo, V, W, Ta, Ni, Mg, Ca, Y, Zr, La and Ce are optional elements, and it
is preferred that "Nb: 0.001% to 0.500%," "Mo: 0.001% to 0.500%," "V: 0.001% to 0.500%,"
"W: 0.001% to 0.500%," "Ta: 0.001% to 0.500%," "Ni: 0.001% to 0.500%," "Mg: 0.001%
to 0.500%," "Ca: 0.001% to 0.500%," "Y: 0.001% to 0.500%," "Zr: 0.001% to 0.500%,"
"La: 0.001% to 0.500%," or "Ce: 0.001% to 0.500%," or any combination thereof be satisfied.
[0041] Next, the coefficient of micro-friction of ferrite on the surface of the high-carbon
steel sheet according to the embodiment is explained. The coefficient of micro-friction
of ferrite on the surface of the high-carbon steel sheet according to the embodiment
is less than 0.5.
(Coefficient of micro-friction of ferrite on the surface: less than 0.5)
[0042] The coefficient of micro-friction of ferrite on the surface closely relates to adhesion
of the high-carbon steel sheet to the metal mold during forming. When the coefficient
of micro-friction of ferrite is 0.5 or more, micro-adhesion occurs between the high-carbon
steel sheet and the metal mold during forming using the metal mold. As a result, when
forming such as punching is performed with several thousands to several tens of thousands
of shots by using the metal mold, adhesive matters are accumulated on the metal mold
during the forming, and a flaw occurs on either the metal mold or the high-carbon
steel sheet or on the both and formability deteriorates. Thus, the coefficient of
micro-friction of ferrite is less than 0.5. From the viewpoint of formability, the
coefficient of micro-friction is the lower the better. The coefficient of micro-friction
often tends to be 0.35 or more, though it depends on a method of manufacturing the
high-carbon steel sheet and others.
[0043] Fig. 2 is a chart illustrating a relationship between a coefficient of micro-friction
of ferrite and a number of pressing (shots) until a flaw occurs on a metal mold or
a high-carbon steel sheet in punch forming of high-carbon steel sheets. As illustrated
in Fig. 2, when the coefficient of micro-friction is less than 0.5, the number of
pressing until a flaw occurs is significantly high as compared to the case when it
is 0.5 or more.
[0044] A coefficient of micro-friction may be measured using a nanoindenter. That is, a
kinetic friction force F to occur when a diamond indenter loads a normal load P of
10 µN onto a surface of a high-carbon steel sheet and is moved horizontally is obtained.
A moving speed then is 1 µm/second, for example. A coefficient of micro-friction µ
(kinetic friction coefficient) is calculated by Expression (1) below. "TI-900 TriboIndenter"
made by Omicron, Inc. may be used as a nanoindenter, for example.

[0045] Fig. 3A is a micrograph showing a surface of a high-carbon steel sheet before measuring
a coefficient of micro-friction, and Fig. 3B is a micrograph showing the surface of
the high-carbon steel sheet after measuring the coefficient of micro-friction. Fig.
3A and Fig. 3B each show an example of a 10 µm × 10 µm visual field. As shown in Fig.
3A and Fig. 3B, ferrite 31 and cementite 32 exist in the visual field example. Further,
as shown in Fig. 3B, measurement flaws 33 caused by horizontal movement of the diamond
indenter exist after the measurement. The coefficient of micro-friction of cementite
was 0.4 or less.
[0046] Next, a structure of the high-carbon steel sheet according to the embodiment is explained.
The high-carbon steel sheet according to the embodiment includes a structure represented
by a spheroidized ratio of cementite: 80% or more and an average diameter of cementite:
0.3 µm to 2.2 µm.
(Spheroidized ratio of cementite: 80% or more)
[0047] Stress concentration sometimes originates from cementite during forming, and stress
is likely to concentrate locally in acicular cementite particularly. When the spheroidized
ratio of cementite is less than 80%, acicular cementite, in which stress is likely
to concentrate, is contained in large amounts, and thus stress concentration occurs
easily and peeling occurs at an interface between ferrite and cementite, resulting
in that sufficient formability cannot be obtained. Thus, the spheroidized ratio of
cementite is 80% or more, and preferably 85% or more. From the viewpoint of formability,
the spheroidized ratio of cementite is preferred to be as higher as possible, and
may be 100%. However, when the spheroidized ratio of cementite is attempted to become
100%, productivity could decrease, and the spheroidized ratio of cementite is preferably
80% or more and less than 100% from the viewpoint of productivity.
(Average diameter of cementite: 0.3 µm to 2.2 µm)
[0048] The average diameter of cementite closely relates to the degree of the stress concentration
to cementite. When the average diameter of cementite is less than 0.3 µm, an Orowan
loop is formed by dislocation occurred during forming with respect to cementite, and
thereby a dislocation density in the vicinity of cementite increases and voids occur.
Thus, the average diameter of cementite is 0.3 µm or more, and preferably 0.5 µm or
more. When the average diameter of cementite is greater than 2.2 µm, dislocations
occurred during forming are accumulated in large amounts, local stress concentration
is generated and a crack occurs. Thus, the average diameter of cementite is 2.2 µm
or less, and preferably 2.0 µm or less.
[0049] The spheroidized ratio and the average diameter of cementite may be measured by structure
observation using a scanning electron microscope. In preparing of a sample for structure
observation, an observation surface is mirror finished by wet polishing with an emery
paper and polishing with diamond abrasive grains having a size of 1 µm, then the observation
surface is etched with an etching solution of 3 vol% of nitric acid and 97 vol% of
alcohol. An observation magnification is between 3000 times to 10000 times, for example,
10000 times, 16 visual fields where 500 or more grains of cementite exist on the observation
surface are selected, and structure images of them are taken. Then, an area of each
cementite in the structure image is measured by using image processing software. "Win
ROOF" made by MITANI Corporation may be used as an image processing software, for
example. Any cementite grain having an area of 0.01 µm
2 or less is excluded from the target of evaluation in order to suppress an influence
of measurement error by noise in the measuring. Then, the average area of cementite
as an evaluation target is obtained, and the diameter of a circle with which this
average area can be obtained is obtained, thereby taking this diameter as the average
diameter of cementite. The average area of cementite is a value obtained by dividing
the total area of cementite as the evaluation target by the number of grains of cementite
in question. Further, any cementite having a ratio of major axis length to minor axis
length of 3 or more is assumed as an acicular cementite, any cementite having the
ratio of less than 3 is assumed as a spherical cementite grain, and a value obtained
by dividing the number of spherical cementite by the number of all cementite is taken
as the spheroidized ratio of cementite.
[0050] Next, a method of manufacturing the high-carbon steel sheet according to the embodiment
is explained. The manufacturing method includes hot-rolling of a slab including the
above chemical composition so as to obtain a hot-rolled steel sheet, pickling of the
hot-rolled steel sheet, and thereafter annealing of the hot-rolled steel sheet. In
the hot-rolling, the slab is heated at a temperature of 1000°C or more and less than
1150°C, a finish rolling temperature is 830°C or more and 950°C or less, and a coiling
temperature is 450°C or more and 700°C or less. In the annealing, the hot-rolled steel
sheet is retained at a temperature of 730°C or more and 770°C or less for 3 hours
or more and 60 hours or less, and then, the hot-rolled steel sheet is cooled down
to 650°C at a cooling rate of 1°C/hr or more and 60°C/hr or less. An atmosphere of
the annealing may be one containing hydrogen by 75 vol% or more at a temperature higher
than 400°C, for example, but is not limited to that.
[0051] Here, an outline of changes in the steel sheet from the hot-rolling to the cooling
is explained. Fig. 4 is a schematic diagram illustrating changes in temperature. Fig.
5A to Fig. 5E are schematic diagrams illustrating changes in structure.
[0052] In an example illustrated in Fig. 4, hot-rolling S1 includes slab heating S11, finish
rolling S12, and coiling S13, and annealing S3 includes high-temperature retention
S31 and cooling S32. Pickling S2 is performed between the hot-rolling S1 and the annealing
S3, and after cooling S4 is performed the annealing S3.
[0053] At a time t
A after completion of the slab heating S11, B atoms 13 segregate to an interface between
austenite 12 and austenite 12, as illustrated in Fig. 5A. At a time t
B after completion of the high-temperature retention S31, the structure of the steel
sheet contains ferrite 11 and the austenite 12, as illustrated in Fig. 5B. Further,
the B atoms 13 segregate to an interface between the ferrite 11 and the austenite
12. Some of the B atoms 13 are present also on a surface 15 of the steel sheet, and
the B atoms 13 present on the surface of the steel sheet are bonded to each other
by covalent bonding 14. Although not illustrated in Fig. 5B, cementite is also contained
in the structure of the steel sheet and some of the B atoms 13 segregate also to an
interface between the ferrite 11 and the cementite. At a time t
C in a middle of the cooling S32, the ratio of the ferrite 11 increases and the ratio
of the austenite 12 decreases as compared to the structure illustrated in Fig. 5B,
as illustrated in Fig. 5C, and the interface between these two phases moves due to
the increasing and decreasing or the ratios. Also, the B atoms 13 present on the surface
of the steel sheet increase with the movement of the interface. Further, at a time
t
D when the cooling S32 has advanced, the ratio of the ferrite 11 increases, the ratio
of the austenite 12 decreases, and the B atoms 13 present on the surface of the steel
sheet increase as compared to the structure illustrated in Fig. 5C, as illustrated
in Fig. 5D. Then, at a time t
E when the temperature of the steel sheet has reached 650°C, the austenite 12 disappears
and the surface 15 of the steel sheet is covered with many of the B atoms 13, as illustrated
in Fig. 5E. Since the B atoms 13 are bonded to each other by the covalent bonding
14, they are crystallized. The structure illustrated in Fig. 5E does not change also
during the cooling S4, and is maintained even when the temperature of the steel sheet
has reached room temperature, for example, a temperature of less than 600°C.
[0054] According to the manufacturing method, the surface 15 of the steel sheet is covered
with many of the B atoms 13 bonded to each other by the covalent bonding 14, and thereby
the coefficient of micro-friction of ferrite on the surface 15 can be less than 0.5.
(Slab heating temperature: 1000°C or more and less than 1150°C)
[0055] When the slab heating temperature is higher than 1150°C, oxygen easily diffuses into
the inside of the slab from the surface of the slab to bond to B in the slab. That
is, as illustrated in Fig. 6A, the B atoms 13 are consumed due to bonding to O atoms
16. Therefore, even though a process thereafter is performed appropriately, it is
not possible to obtain a good surface covered with crystals of B, resulting in that
the coefficient of micro-friction of ferrite on the surface cannot be less than 0.5.
Thus, the slab heating temperature is 1150°C or less, and preferably 1140°C or less.
When the slab heating temperature is lower than 1000°C, micro-segregation and/or macro-segregation
formed during casting cannot be eliminated, and as illustrated in Fig. 6B, solidification
segregations of the B atoms 13 remain. The solidification segregations of the B atoms
13 cannot be eliminated even though a process thereafter is performed appropriately,
and therefore, it is not possible to obtain a good surface covered with crystals of
B, resulting in that the coefficient of micro-friction of ferrite on the surface cannot
be less than 0.5. Further, when the slab heating temperature is lower than 1000°C,
regions where Cr atoms and/or Mn atoms segregate and concentrate also remain in the
high-carbon steel sheet. Therefore, even though a process thereafter is performed
appropriately, cracks occur from the regions during forming, thus making it impossible
to obtain good formability. Thus, the slab heating temperature is 1000°C or more,
and preferably 1030°C or more.
(Finish rolling temperature: 830°C or more and 950°C or less)
[0056] When the finish rolling temperature is higher than 950°C, coarse scales are generated
until completion of coiling on a run out table (ROT), for example. The coarse scales
can be removed by pickling, but traces of large irregularities are left, resulting
in that adhesion to the metal mold sometimes occurs during forming due to the traces.
Further, when coarse scales are generated, irregular flaw is caused on the surface
of the steel sheet in the coiling, resulting in that due to the flaw, adhesion to
the metal mold sometimes occurs during forming. Thus, the finish rolling temperature
is 950°C or less, and preferably 940°C or less. When the finish rolling temperature
is lower than 830°C, adhesiveness of scales generated until completion of coiling
to the steel sheet is extremely high, thus making it difficult to remove the scales
by pickling. The scales may be removed by performing strong pickling, but the strong
pickling makes the surface of the steel sheet rough, resulting in that adhesion to
the metal mold sometimes occurs during forming. Further, when the finish rolling temperature
is lower than 830°C, recrystallization of austenite is not completed by the coiling,
so that anisotropy of the hot-rolled steel sheet increases. The anisotropy of the
hot-rolled steel sheet is carried over even after annealing, and thus sufficient formability
cannot be obtained. Thus, the finish rolling temperature is 830°C or more, and preferably
840°C or more.
(Coiling temperature: 450°C or more and 700°C or less)
[0057] When the coiling temperature is higher than 700°C, coarse lamellar pearlite is formed
in the hot-rolled steel sheet to hinder spheroidizing of cementite during annealing,
resulting in that the spheroidized ratio of 80% or more cannot be obtained. Thus,
the coiling temperature is 700°C or less. Further, when the coiling temperature is
higher than 570°C, coarse scales are generated until completion of coiling. Therefore,
adhesion to the metal mold sometimes occurs during forming for a reason similar to
the case where the finish rolling temperature is higher than 950°C. Thus, the coiling
temperature is preferably 570°C or less, and further preferably 550°C or less. When
the coiling temperature is lower than 450°C, adhesiveness of scales generated until
completion of coiling to the steel sheet is extremely high, thus making it difficult
to remove the scales by pickling. The scales may be removed by performing strong pickling,
but the strong pickling makes the surface of the steel sheet rough, resulting in that
adhesion to the metal mold sometimes occurs during forming. Further, when the coiling
temperature is lower than 450°C, the hot-rolled steel sheet becomes brittle and the
hot-rolled steel sheet may crack when a coil is uncoiled in pickling, resulting in
that a sufficient yield cannot be obtained. Thus, the coiling temperature is 450°C
or more, and preferably 460°C or more.
[0058] A rough-rolled bar may be heated near an inlet of a finishing mill in order to ensure
qualities in a longitudinal direction and a width direction of a hot-rolled coil obtained
by coiling(to reduce variation of quality or the like). An apparatus to be used for
the heating and a method of the heating are not limited in particular, but heating
by high-frequency induction heating is desirably performed. A preferred temperature
range of the heated rough-rolled bar is between 850°C and 1100°C. Temperatures less
than 850°C are close to a transformation temperature from austenite to ferrite, and
therefore, when the temperature of the heated rough bar is lower than 850°C, heat
generation and heat absorption due to transformation and reverse transformation sometimes
occur, resulting in that temperature controlling is unstable and it is difficult to
uniformize a temperatures in the longitudinal direction and the width direction of
the hot-rolled coil. Therefore, if the rough-rolled bar is heated, the heating temperature
is preferably 850°C or more. Increasing the temperature of the rough-rolled bar to
temperature higher than 1100°C takes excessive time, and the productivity decreases.
Therefore, if rough-rolled bar is heated, the heating temperature is preferably 1100°C
or less.
(Annealing retention temperature: 730°C or more and 770°C or less)
[0059] When the annealing retention temperature is lower than 730°C, the austenite 12 is
not formed sufficiently, and as illustrated in Fig. 6C, although a large number of
interfaces between the ferrite 11 and the ferrite 11 exist, sites where the B atom
13 segregates are insufficient. Therefore, even though a process thereafter is performed
appropriately, a good surface covered with crystals of B cannot be obtained, resulting
in that the coefficient of micro-friction of ferrite on the surface cannot be less
than 0.5. Further, when the annealing retention temperature is lower than 730°C, segregation
of the B atom 13 to the interface between the ferrite 11 and cementite does not occur
easily, and therefore, segregating the B atoms 13 sufficiently takes an extremely
long time, which is about 100 hours, and the productivity decreases. Thus, the annealing
retention temperature is 730°C or more, and preferably 735°C or more. When the annealing
retention temperature is higher than 770°C, as illustrated in Fig. 6D, the B atoms
13 concentrate and coarse crystals of B are formed in the vicinity of the triple point
of the ferrite 11, the austenite 12, and the surface of the steel sheet. When coarse
crystals of B are formed, even though a process thereafter is performed appropriately,
the thickness of a film of the crystals of B varies greatly, resulting in that the
coefficient of micro-friction of ferrite on the surface cannot be less than 0.5. Further,
when the annealing retention temperature is higher than 770°C, thermal expansion of
the hot-rolled steel sheet coiled in a coil shape is large, and the hot-rolled steel
sheet itself sometimes rubs together during annealing to cause abrasions on the surface.
The appearance of the surface is impaired and the yield is decreased by the abrasions.
Thus, the annealing retention temperature is 770°C or less, and preferably 765°C or
less.
(Annealing retention time: 3 hours or more and 60 hours or less)
[0060] When the annealing retention time is less than 3 hours, as illustrated in Fig. 6E,
the B atoms 13 do not sufficiently segregate to the interface between the ferrite
11 and the austenite 12, and therefore, even though a process thereafter is performed
appropriately, a good surface covered with crystals of B cannot be obtained, resulting
in that the coefficient of micro-friction of ferrite on the surface cannot be less
than 0.5. Further, when the annealing retention time is less than 3 hours, cementite
does not become coarse sufficiently, resulting in that the average diameter of cementite
cannot be 0.3 µm or more. Thus, the annealing retention time is 3 hours or more, and
preferably 5 hours or more. When the annealing retention time is greater than 60 hours,
the coefficient of micro-friction of ferrite on the surface cannot be less than 0.5
for a reason similar to the case where the annealing retention temperature is higher
than 770°C. Further, when the annealing retention time is greater than 60 hours, cementite
becomes coarse excessively, resulting in that the average diameter of cementite cannot
be 2.2 µm or less. Thus, the annealing retention time is 60 hours or less, and preferably
40 hours or less.
(Cooling rate down to 650°C: 1°C/hr or more and 60°C /hr or less)
[0061] When the cooling rate down to 650°C is less than 1°C/hr, as illustrated in Fig. 6F,
crystals of B are formed excessively during cooling and the crystals of B form a projection
on the surface of the high-carbon steel sheet. Once a projection is formed, the thickness
of the film of the crystals of B varies greatly, resulting in that adhesion to the
metal mold occurs during forming and a flaw occurs on the metal mold. Further, when
the cooling rate down to 650°C is less than 1°C/hr, sufficient productivity cannot
be obtained. Thus, the cooling rate down to 650°C is 1°C/hr or more, and preferably
2°C/hr or more. When the cooling rate down to 650°C is greater than 60°C/hr, a decrease
rate of the austenite 12 is excessive, and as illustrated in Fig. 6G, the sufficient
covalent bonding 14 cannot be caused between the B atoms 13, resulting in that the
coefficient of micro-friction of ferrite on the surface cannot be less than 0.5. Further,
when the cooling rate down to 650°C is greater than 60°C/hr, pearlite is formed from
the austenite 12 during cooling to hinder spheroidizing of cementite, resulting in
that the spheroidized ratio of 80% or more cannot be obtained. Thus, the cooling rate
down to 650°C is 60°C/hr or less, and 50°C/or less.
[0062] According to the embodiment, excellent lubricity can be obtained, and therefore it
is possible to suppress adhesion of the high-carbon steel sheet to the metal mold
and suppress wearing of the metal mold. Further, according to the embodiment, it is
also possible to suppress cracking during forming.
[0063] It should be noted that all of the above-described embodiments merely illustrate
concrete examples of implementing the present invention, and the technical scope of
the present invention is not to be construed in a restrictive manner by these embodiments.
That is, the present invention may be implemented in various forms without departing
from the technical spirit or main features thereof.
EXAMPLE
[0064] Next, examples of the present invention will be described. Conditions in the examples
are condition examples employed for confirming feasibility and effect of the present
invention, and the present invention is not limited to these condition examples. The
present invention can employ various conditions as long as the object of the present
invention is achieved without departing from the spirit of the invention.
(First experiment)
[0065] In a first experiment, hot-rolling of a slab (Steel type A to Y, BK) including a
chemical composition listed in Table 1 was performed, thereby obtaining a hot-rolled
steel sheet having a thickness of 4 mm. In the hot-rolling, the slab heating temperature
was 1130°C, the time thereof was 1 hour, the finish rolling temperature was 850°C,
and the coiling temperature was 520°C. Then, cooling was performed down to a temperature
of less than 60°C, and pickling using sulfuric acid was performed. Thereafter, annealing
of the hot-rolled steel sheet was performed to then obtain a hot-rolled annealed steel
sheet. In the annealing, the hot-rolled steel sheet was retained for 15 hours at 750°C,
and then was cooled down to 650°C at a cooling rate of 30°C/hr. Subsequently, cooling
was performed down to a temperature of less than 60°C. In this manner, various high-carbon
steel sheets were manufactured. Blank fields in Table 1 indicate that the content
of the element is less than a detection limit, and the balance is Fe and impurities.
For example, the Cr content of Steel type BK may be regarded as 0.00%.
[0066] An underline in Table 1 indicates that the numeric value is out of the range of the
present invention.

[0067] Then, the coefficient of micro-friction of ferrite, and the spheroidized ratio and
the average diameter of cementite of each of the high-carbon steel sheets were measured.
A friction coefficient of cementite was also measured in measuring the coefficient
of micro-friction of ferrite. Results of them are listed in Table 2. An underline
in Table 2 indicates that the item is out of the range of the present invention.
[0068] Further, evaluation of adhesion suppressive performance and evaluation of crack sensitivity
of each of the high-carbon steel sheets were performed as formability evaluation.
In the evaluation of adhesion suppressive performance, a draw bead test was performed.
That is, an indentation bead with a tip having a 20 mm radius R was pressed against
the high-carbon steel sheet with a load of 10 kN and was pulled out. Then, presence
or absence of adhesive matter on the tip of the indentation bead was observed, and
one with presence of adhesive matter was evaluated as × and one with no presence was
evaluated as ○. The presence of adhesive matter in this test indicates that in press
forming with several thousands to several tens of thousands of shots, an adhesive
matter occurs early on the metal mold to deteriorate formability. In the evaluation
of crack sensitivity, a compression test was performed. That is, a cylindrical test
piece having a 10 mm diameter and a 4 mm height was cut out from the high-carbon steel
sheet so that a height direction of the test piece was parallel to a sheet thickness
direction, and the test piece was compressed to 1 mm in height. Then, an appearance
observation and a sectional structure observation were performed, and then one in
which cracking appeared in the appearance during compression or after compression
and one in which a crack of 1 mm or more was present in the sectional structure observation
were evaluated as ×, and one other than the above was evaluated as ○. Results of them
are also listed in Table 2.
[Table 2]
SAMPLE No. |
STEEL TYPE |
COEFFICIENT OF MICRO-FRICTION OF FERRITE |
COEFFICIENT OF MICRO-FRICTION OF CEMENTITE |
SPHEROIDIZED RATIO OF CEMENTITE (%) |
AVERAGE DIAMETER OF CEMENTITE (µm) |
ADHESION SUPPRESSIVE PERFORMANCE |
CRACK SENSITIVITY |
REMARKS |
1 |
A |
0.40 |
0.24 |
80.4 |
0.76 |
○ |
○ |
INVENTIVE EXAMPLE |
2 |
B |
0.43 |
0.25 |
80,4 |
1.13 |
○ |
○ |
INVENTIVE EXAMPLE |
3 |
C |
0.40 |
0.31 |
86.5 |
0.62 |
○ |
○ |
INVENTIVE EXAMPLE |
4 |
D |
0.42 |
0.23 |
83.8 |
0.86 |
○ |
○ |
INVENTIVE EXAMPLE |
5 |
E |
0.42 |
0.32 |
95.5 |
0.69 |
○ |
○ |
INVENTIVE EXAMPLE |
6 |
F |
0.41 |
0.33 |
90.0 |
0.42 |
○ |
○ |
INVENTIVE EXAMPLE |
7 |
G |
0.49 |
0.23 |
85.4 |
0.96 |
○ |
○ |
INVENTIVE EXAMPLE |
8 |
H |
0.44 |
0.28 |
98.7 |
0.52 |
○ |
○ |
INVENTIVE EXAMPLE |
9 |
I |
0.42 |
0.33 |
94.8 |
0.56 |
○ |
○ |
INVENTIVE EXAMPLE |
10 |
J |
0.42 |
0.32 |
92.6 |
0.56 |
× |
○ |
COMPARATIVE EXAMPLE |
11 |
K |
0.72 |
0.25 |
91.4 |
0.59 |
× |
× |
COMPARATIVE EXAMPLE |
12 |
L |
0.42 |
0.23 |
81.7 |
0.85 |
○ |
× |
COMPARATIVE EXAMPLE |
13 |
M |
0.42 |
0.29 |
85.9 |
0.73 |
○ |
× |
COMPARATIVE EXAMPLE |
14 |
N |
0.41 |
0.30 |
75.6 |
1.04 |
○ |
× |
COMPARATIVE EXAMPLE |
15 |
O |
0.42 |
0.31 |
90.9 |
0.36 |
○ |
× |
COMPARATIVE EXAMPLE |
16 |
P |
0.41 |
0.23 |
82.4 |
0.54 |
○ |
× |
COMPARATIVE EXAMPLE |
17 |
Q |
0.79 |
0.24 |
87.7 |
1.05 |
× |
× |
COMPARATIVE EXAMPLE |
18 |
R |
0.79 |
0.33 |
92.5 |
0.55 |
× |
× |
COMPARATIVE EXAMPLE |
19 |
S |
0.44 |
0.27 |
85.2 |
2.56 |
○ |
× |
COMPARATIVE EXAMPLE |
20 |
T |
0.41 |
0.31 |
91.2 |
0.71 |
○ |
× |
COMPARATIVE EXAMPLE |
21 |
U |
0.41 |
0.28 |
98.0 |
0.52 |
○ |
× |
COMPARATIVE EXAMPLE |
22 |
V |
0.44 |
0.31 |
65.8 |
026 |
○ |
× |
COMPARATIVE EXAMPLE |
23 |
W |
0.45 |
0.25 |
98.9 |
0.30 |
○ |
× |
COMPARATIVE EXAMPLE |
24 |
X |
0.62 |
0.28 |
85.3 |
0.75 |
× |
× |
COMPARATIVE EXAMPLE |
25 |
Y |
0.42 |
0.27 |
82.2 |
0.59 |
○ |
× |
COMPARATIVE EXAMPLE |
26 |
BK |
0.69 |
0.29 |
80.6 |
0.92 |
× |
○ |
COMPARATIVE EXAMPLE |
[0069] As listed in Table 2, Sample No. 1 to Sample No. 9 were each within the range of
the present invention, thus being able to obtain good adhesion suppressive performance
and crack sensitivity.
[0070] On the other hand, in Sample No. 10, the C content of Steel type J was too low, and
thus the amount of cementite was insufficient, sufficient lubricity was not able to
be obtained, and adhesion to the metal mold occurred during forming. In Sample No.
11, the N content of Steel type K was too high, and thus BN precipitated, the amount
of solid-solution B was insufficient, the coefficient of micro-friction of ferrite
was low, and adhesion and cracking during the compression test occurred. In Sample
No. 12, the Al content of Steel type L was too high, and thus the ductility of ferrite
was low and a crack originating from transgranular fracture of ferrite occurred during
the compression test. In Sample No. 13, the B content of Steel type M was too high,
and thus boride was formed and a crack originating from the boride is occurred during
the compression test. In Sample No. 14, the Mn content of Steel type N was too low,
and thus pearlite transformation occurred during cooling in the annealing, the spheroidized
ratio of cementite was low, and a crack originating from acicular cementite occurred
during the compression test. In Sample No. 15, the P content of Steel type O was too
high, and thus segregation of B to the interface between ferrite and cementite was
hindered and cracking occurred during the compression test. In Sample No. 16, the
Si content of Steel type P was too high, and thus the ductility of ferrite was low
and a crack originating from transgranular fracture of ferrite occurred during the
compression test. In Sample No. 17 and Sample No. 18, each B content of Steel type
Q and Steel type R was too low, and thus the coefficient of micro-friction of ferrite
was low and adhesion and cracking during the compression test occurred. In Sample
No. 19, the Si content of Steel type S was too low, and thus cementite became coarse
excessively during annealing and a crack originating from the coarse cementite occurred
during the compression test. In Sample No. 20, the S content of Steel type T was too
high, and thus coarse sulfides being non-metal inclusions were formed and a crack
originating from the coarse sulfide occurred during the compression test. In Sample
No. 21, the Mn content of Steel type U was too high, and thus the ductility of ferrite
was low and a crack originating from transgranular fracture of ferrite occurred during
the compression test. In Sample No. 22, the Cr content of Steel type V was too high,
and thus spheroidizing of cementite during annealing was hindered, coarsening of cementite
was suppressed, and a crack originating from micro acicular cementite occurred during
the compression test. In Sample No. 23, the C content of Steel type W was too high,
and thus the amount of cementite was excessive and a crack originating from the cementite
occurred during the compression test. In Sample No. 24, the Ti content of Steel type
X was too low, and thus BN precipitated, the amount of solid-solution B was insufficient,
the coefficient of micro-friction of ferrite was low, and adhesion and cracking during
the compression test occurred. In Sample No. 25, the Ti content of Steel type Y was
too high, and thus coarse oxides of Ti were formed and a crack originating from the
coarse oxide of Ti occurred during the compression test. In Sample No. 26, the Cr
content of Steel type BK was too low, and thus BN precipitated, the amount of solid-solution
B was insufficient, the coefficient of micro-friction of ferrite was low, and adhesion
to the metal mold occurred during forming.
(Second experiment)
[0071] In a second experiment, hot-rolling of a slab (Steel type Z to BJ) including a chemical
composition listed in Table 3 was performed, thereby obtaining a hot-rolled steel
sheet having a thickness of 4 mm.
[0072] In the hot-rolling, the slab heating temperature was 1130°C, the time thereof was
1 hour, the finish rolling temperature was 850°C, and the coiling temperature was
520°C. Then, cooling was performed down to a temperature of less than 60°C, and pickling
using sulfuric acid was performed. Thereafter, annealing of the hot-rolled steel sheet
was performed to then obtain a hot-rolled annealed steel sheet. In the annealing,
the hot-rolled steel sheet was retained for 15 hours at 750°C, and then was cooled
down to 650°C at a cooling rate of 30°C /hr. Subsequently, cooling was performed down
to a temperature of less than 60°C. In this manner, various high-carbon steel sheets
were manufactured. Blank fields in Table 3 indicate that the content of the element
is less than a detection limit, and the balance is Fe and impurities. An underline
in Table 3 indicates that the numeric value is out of the range of the present invention.

[0073] Then, in the same manner as in the first experiment, the coefficient of micro-friction
of ferrite, and the spheroidized ratio and the average diameter of cementite of each
of the high-carbon steel sheets were measured, and further, the evaluation of adhesion
suppressive performance and the evaluation of crack sensitivity were performed. Results
of them are listed in Table 4. An underline in Table 4 indicates that the item is
out of the range of the present invention.
[Table 4]
SAMPLE No. |
STEEL TYPE |
COEFFICIENT OF MICRO-FRICTION OF FERRITE |
COEFFICIENT OF MICRO-FRICTION OF CEMENTITE |
SPHEROIDIZED RATIO OF CEMENTITE (%) |
AVERAGE DIAMETER OF CEMENTITE (µm) |
ADHESION SUPPRESSIVE PERFORMANC E |
CRACK SENSITIVITY |
REMARKS |
31 |
Z |
0.43 |
0.28 |
90.8 |
0.45 |
○ |
○ |
INVENTIVE EXAMPLE |
32 |
AA |
0.43 |
0.23 |
85.2 |
0.41 |
○ |
○ |
INVENTIVE EXAMPLE |
33 |
AB |
0.41 |
0.27 |
80.2 |
0.98 |
○ |
○ |
INVENTIVE EXAMPLE |
34 |
AC |
0.45 |
0.32 |
81.4 |
2.05 |
○ |
○ |
INVENTIVE EXAMPLE |
35 |
AD |
0.41 |
0.28 |
86.4 |
0.62 |
○ |
○ |
INVENTIVE EXAMPLE |
36 |
AE |
0.43 |
0.31 |
82.3 |
1.24 |
○ |
○ |
INVENTIVE EXAMPLE |
37 |
AF |
0.42 |
0.23 |
84.5 |
1.02 |
○ |
○ |
INVENTIVE EXAMPLE |
38 |
AG |
0.43 |
0.30 |
91.2 |
0.31 |
○ |
○ |
INVENTIVE EXAMPLE |
39 |
AH |
0.42 |
0.28 |
82.2 |
1.71 |
○ |
○ |
INVENTIVE EXAMPLE |
40 |
AI |
0.42 |
0.31 |
94.1 |
0.31 |
○ |
○ |
INVENTIVE EXAMPLE |
41 |
AJ |
0.43 |
0.26 |
91.3 |
0.89 |
○ |
○ |
INVENTIVE EXAMPLE |
42 |
AK |
0.40 |
0.34 |
93.9 |
0.64 |
○ |
○ |
INVENTIVE EXAMPLE |
43 |
AL |
0.41 |
0.24 |
87.2 |
0.39 |
○ |
○ |
INVENTIVE EXAMPLE |
44 |
AM |
0.43 |
0.31 |
90.5 |
0.45 |
× |
○ |
COMPARATIVE EXAMPLE |
45 |
AN |
0.45 |
0.30 |
85.4 |
0.36 |
× |
○ |
COMPARATIVE EXAMPLE |
46 |
AO |
0.45 |
0.25 |
83.0 |
0.75 |
○ |
× |
COMPARATIVE EXAMPLE |
47 |
AP |
0.44 |
0.26 |
86.3 |
0.64 |
○ |
× |
COMPARATIVE EXAMPLE |
48 |
AQ |
0.58 |
0.25 |
85.2 |
0.54 |
× |
× |
COMPARATIVE EXAMPLE |
49 |
AR |
0.42 |
0.31 |
89.1 |
0.42 |
○ |
× |
COMPARATIVE EXAMPLE |
50 |
AS |
0.40 |
0.23 |
79.0 |
1.39 |
○ |
× |
COMPARATIVE EXAMPLE |
51 |
AT |
0.44 |
0.33 |
85.7 |
1.35 |
○ |
× |
COMPARATIVE EXAMPLE |
52 |
AU |
0.44 |
0.32 |
84.0 |
0.43 |
○ |
× |
COMPARATIVE EXAMPLE |
53 |
AV |
0.73 |
0.25 |
98.1 |
0.56 |
× |
○ |
COMPARATIVE EXAMPLE |
54 |
AW |
0.44 |
0.23 |
80.9 |
0.52 |
○ |
× |
COMPARATIVE EXAMPLE |
55 |
AX |
0.42 |
0.27 |
84.7 |
1.82 |
○ |
× |
COMPARATIVE EXAMPLE |
56 |
AY |
0.41 |
0.30 |
64.0 |
0.24 |
○ |
× |
COMPARATIVE EXAMPLE |
57 |
AZ |
0.43 |
0.23 |
67.4 |
1.05 |
○ |
× |
COMPARATIVE EXAMPLE |
58 |
BA |
0.43 |
0.28 |
92.9 |
0.57 |
○ |
× |
COMPARATIVE EXAMPLE |
59 |
BB |
0.42 |
0.31 |
89.6 |
0.80 |
○ |
× |
COMPARATIVE EXAMPLE |
60 |
BC |
0.42 |
0.22 |
92.0 |
0.42 |
○ |
× |
COMPARATIVE EXAMPLE |
61 |
BD |
0.46 |
0.23 |
95.0 |
0.46 |
○ |
× |
COMPARATIVE EXAMPLE |
62 |
BE |
0.69 |
0.27 |
89.6 |
0.58 |
× |
× |
COMPARATIVE EXAMPLE |
63 |
BF |
0.43 |
0.31 |
90.6 |
2.32 |
○ |
× |
COMPARATIVE EXAMPLE |
64 |
BG |
0.44 |
0.22 |
96.7 |
0.73 |
○ |
× |
COMPARATIVE EXAMPLE |
65 |
BH |
0.42 |
0.32 |
85.0 |
0.37 |
○ |
× |
COMPARATIVE EXAMPLE |
66 |
BI |
0.41 |
0.29 |
98.9 |
0.63 |
○ |
× |
COMPARATIVE EXAMPLE |
67 |
BJ |
0.42 |
0.25 |
88.3 |
1.64 |
○ |
× |
COMPARATIVE EXAMPLE |
[0074] As listed in Table 4, Samples No. 31 to No. 43 were each within the range of the
present invention, thus being able to obtain good adhesion suppressive performance
and crack sensitivity.
[0075] On the other hand, in Sample No. 44, the C content of Steel type AM was too low,
and thus the amount of cementite was insufficient, sufficient lubricity was not able
to be obtained, and adhesion to the metal mold occurred during forming. In Sample
No. 45, the Cu content of Steel type AN was too high, and thus a flaw occurred during
hot-rolling and adhesion originating from the flaw occurred. In Sample No. 46, the
Ca content of Steel type AO was too high, and thus coarse oxides of Ca were formed
and a crack originating from the coarse oxide of Ca occurred during the compression
test. In Sample No. 47, the Mo content of Steel type AP was too high, and thus the
ductility of ferrite was low and a crack originating from transgranular fracture of
ferrite occurred during the compression test. In Sample No. 48, the B content of Steel
type AQ was too low, and thus the coefficient of micro-friction of ferrite was low
and adhesion and cracking during the compression test occurred. In Sample No. 49,
the Nb content of Steel type AR was too high, and thus the ductility of ferrite was
low and a crack originating from transgranular fracture of ferrite occurred during
the compression test. In Sample No. 50, the Mn content of Steel type AS was too low,
and thus pearlite transformation occurred during cooling in the annealing, the spheroidized
ratio of cementite was low, and a crack originating from acicular cementite occurred
during the compression test. In Sample No. 51, the Ce content of Steel type AT was
too high, and thus coarse oxides of Ce were formed and a crack originating from the
coarse oxide of Ce occurred during the compression test. In Sample No. 52, the B content
of Steel type AU was too high, and thus boride was formed and a crack originating
from the boride occurred during the compression test. In Sample No. 53, the Ni content
of Steel type AV was too high, and thus the coefficient of micro-friction of ferrite
was high and adhesion occurred. In Sample No. 54, the V content of Steel type AW was
too high, and thus the ductility of ferrite was low and a crack originating from transgranular
fracture of ferrite occurred during the compression test. In Sample No. 55, the Zr
content of Steel type AX was too high, and thus coarse oxides of Zr were formed and
a crack originating from the coarse oxide of Zr occurred during the compression test.
In Sample No. 56, the Cr content of Steel type AY was too high, and thus spheroidizing
of cementite during annealing was hindered, coarsening of cementite was suppressed,
and a crack originating from micro acicular cementite occurred during the compression
test. In Sample No. 57, the Mn content of Steel type AZ was too low, and thus pearlite
transformation occurred during cooling in the annealing, the spheroidized ratio of
cementite was low, and a crack originating from acicular cementite occurred during
the compression test. In Sample No. 58, the Y content of Steel type BA was too high,
and thus coarse oxides of Y were formed and a crack originating from the coarse oxide
of Y occurred during the compression test. In Sample No. 59, the La content of Steel
type BB was too high, and thus coarse oxides of La were formed and a crack originating
from the coarse oxide of La occurred during the compression test. In Sample No. 60,
the S content of Steel type BC was too high, and thus coarse sulfides being non-metal
inclusions were formed and a crack originating from the coarse sulfide occurred during
the compression test. In Sample No. 61, the W content of Steel type BD was too high,
and thus the ductility of ferrite was low and a crack originating from transgranular
fracture of ferrite occurred during the compression test. In Sample No. 62, the Ti
content of Steel type BE was too low, and thus BN precipitated, the amount of solid-solution
B was insufficient, the coefficient of micro-friction of ferrite was low, and adhesion
and cracking during the compression test occurred. In Sample No. 63, the Si content
of Steel type BF was too low, and thus cementite became coarse excessively and a crack
originating from the coarse cementite occurred during the compression test. In Sample
No. 64, the P content of Steel type BG was too high, and thus segregation of B to
the interface between ferrite and cementite was hindered and cracking occurred during
the compression test. In Sample No. 65, the Ta content of Steel type BH was too high,
and thus the ductility of ferrite was low and a crack originating from transgranular
fracture of ferrite occurred during the compression test. In Sample No. 66, the Mg
content of Steel type BI was too high, and thus coarse oxides of Mg were formed and
a crack originating from the coarse oxide of Mg occurred during the compression test.
In Sample No. 67, the C content of Steel type BJ was too high, and thus the amount
of cementite was excessive and a crack originating from the cementite occurred during
the compression test.
[0076] Fig. 1 illustrates the relationship between the coefficient of micro-friction of
ferrite and the B content of Samples No. 1 to No. 25 and No. 31 to No. 67 except for
Samples No. 11, No. 51, No. 53, and No. 62. As illustrated in Fig. 1, when the B content
is 0.0004% or more, the coefficient of micro-friction of ferrite is significantly
low as compared to the case when it is less than 0.0004%.
(Third experiment)
[0077] In a third experiment, hot-rolling and annealing were performed under various conditions
on the steel types that were within the range of the present invention (Steel types
A to I and Steel types Z to AL) out of the steel types used in the first experiment
and the steel types used in the second experiment so as to manufacture high-carbon
steel sheets. Conditions of them are listed in Table 5 to Table 7. An underline in
Table 5 to Table 7 indicates that the numeric value is out of the range of the present
invention.
[Table 5]
SAMPLE No. |
STEEL TYPE |
CONDITIONS IN HOT-ROLLING |
CONDITIONS IN ANNEALING |
REMARKS |
SLAB HEATING TEMPERATURE (°C) |
FINISH ROLLING TEMPERATURE (°C) |
COILING TEMPERATURE (°C) |
RETENTION TEMPERATURE (°C) |
RETENTION TIME (hr) |
COLLING RATE (°C/hr) |
71 |
A |
1116 |
871 |
540 |
786 |
51.4 |
56.7 |
COMPARATIVE EXAMPLE |
72 |
B |
1149 |
841 |
646 |
745 |
18.4 |
58.6 |
INVENTIVE EXAMPLE |
73 |
C |
1113 |
879 |
706 |
747 |
9.7 |
26.7 |
COMPARATIVE EXAMPLE |
74 |
D |
1006 |
940 |
681 |
757 |
34.7 |
33.6 |
INVENTIVE EXAMPLE |
75 |
E |
1149 |
889 |
605 |
756 |
2.2 |
13.9 |
COMPARATIVE EXAMPLE |
76 |
F |
993 |
902 |
554 |
759 |
3.6 |
30.7 |
COMPARATIVE EXAMPLE |
77 |
G |
1068 |
891 |
684 |
742 |
26.8 |
3.8 |
INVENTIVE EXAMPLE |
78 |
H |
1044 |
874 |
685 |
736 |
56.2 |
53.2 |
INVENTIVE EXAMPLE |
79 |
I |
1083 |
845 |
590 |
748 |
46.3 |
40.7 |
INVENTIVE EXAMPLE |
80 |
Z |
1120 |
914 |
616 |
751 |
6.5 |
1.3 |
INVENTIVE EXAMPLE |
81 |
AA |
1122 |
880 |
714 |
765 |
43.0 |
58.9 |
COMPARATIVE EXAMPLE |
82 |
AB |
1113 |
844 |
583 |
752 |
55.3 |
2.7 |
INVENTIVE EXAMPLE |
83 |
AC |
1088 |
863 |
695 |
749 |
7.6 |
38.0 |
INVENTIVE EXAMPLE |
84 |
AD |
1065 |
850 |
547 |
741 |
18.3 |
68.1 |
COMPARATIVE EXAMPLE |
85 |
AE |
1095 |
904 |
680 |
750 |
36.5 |
48.6 |
INVENTIVE EXAMPLE |
86 |
AF |
1118 |
949 |
521 |
776 |
57.9 |
7.5 |
COMPARATIVE EXAMPLE |
87 |
AG |
1024 |
859 |
435 |
766 |
58.7 |
5.5 |
COMPARATIVE EXAMPLE |
88 |
AH |
1078 |
874 |
620 |
754 |
18.8 |
21.3 |
INVENTIVE EXAMPLE |
89 |
AI |
1028 |
861 |
615 |
753 |
3.1 |
21.2 |
INVENTIVE EXAMPLE |
90 |
AJ |
1136 |
915 |
689 |
767 |
46.8 |
27.6 |
INVENTIVE EXAMPLE |
91 |
AK |
1098 |
936 |
645 |
760 |
37.1 |
8.1 |
INVENTIVE EXAMPLE |
92 |
AL |
1099 |
901 |
691 |
754 |
29.7 |
12.7 |
INVENTIVE EXAMPLE |
[Table 6]
SAMPLE No. |
STEEL TYPE |
CONDITIONS IN HOT-ROLLING |
CONDITIONS IN ANNEALING |
REMARKS |
SLAB HEATING TEMPERATURE (°C) |
FINISH ROLLING TEMPERATURE (°C) |
COILING TEMPERATURE (°C) |
RETENTION TEMPERATURE (°C) |
RETENTION TIME (hr) |
COLLING RATE (°C/hr) |
101 |
A |
1104 |
873 |
527 |
721 |
38.3 |
32.0 |
COMPARATIVE EXAMPLE |
102 |
B |
1060 |
983 |
560 |
757 |
56.8 |
17.3 |
COMPARATIVE EXAMPLE |
103 |
C |
1129 |
865 |
625 |
732 |
4.9 |
42.7 |
INVENTIVE EXAMPLE |
104 |
D |
1175 |
863 |
548 |
767 |
12.6 |
30.7 |
COMPARATIVE EXAMPLE |
105 |
E |
1109 |
875 |
632 |
749 |
4.6 |
40.7 |
INVENTIVE EXAMPLE |
106 |
F |
1088 |
865 |
677 |
768 |
23.0 |
2.3 |
INVENTIVE EXAMPLE |
107 |
G |
1142 |
869 |
536 |
736 |
5.5 |
62.3 |
COMPARATIVE EXAMPLE |
108 |
H |
1064 |
848 |
640 |
739 |
14.8 |
29.0 |
INVENTIVE EXAMPLE |
109 |
I |
1064 |
847 |
621 |
745 |
7.8 |
24.5 |
INVENTIVE EXAMPLE |
110 |
Z |
1007 |
878 |
656 |
747 |
48.2 |
2.9 |
INVENTIVE EXAMPLE |
111 |
AA |
1051 |
943 |
699 |
768 |
6.2 |
1.2 |
INVENTIVE EXAMPLE |
112 |
AB |
1158 |
908 |
526 |
760 |
6.2 |
7.3 |
COMPARATIVE EXAMPLE |
113 |
AC |
1131 |
823 |
532 |
761 |
47.9 |
16.2 |
COMPARATIVE EXAMPLE |
114 |
AD |
1047 |
847 |
605 |
730 |
22.5 |
25.2 |
INVENTIVE EXAMPLE |
115 |
AE |
1080 |
862 |
648 |
752 |
26.8 |
31.7 |
INVENTIVE EXAMPLE |
116 |
AF |
1102 |
885 |
666 |
741 |
17.0 |
42.8 |
INVENTIVE EXAMPLE |
117 |
AG |
1050 |
932 |
601 |
770 |
32.6 |
1.9 |
INVENTIVE EXAMPLE |
118 |
AH |
1025 |
875 |
540 |
718 |
26.3 |
41.3 |
COMPARATIVE EXAMPLE |
119 |
AI |
1078 |
936 |
625 |
750 |
17.1 |
58.1 |
INVENTIVE EXAMPLE |
120 |
AJ |
1079 |
881 |
671 |
764 |
9.7 |
28.7 |
INVENTIVE EXAMPLE |
121 |
AK |
1084 |
867 |
641 |
735 |
27.8 |
4.5 |
INVENTIVE EXAMPLE |
122 |
AL |
1116 |
890 |
531 |
742 |
4.5 |
9.3 |
INVENTIVE EXAMPLE |
[Table 7]
SAMPLE No. |
STEEL TYPE |
CONDITIONS IN HOT-ROLLING |
CONDITIONS IN ANNEALING |
REMARKS |
SLAB HEATING TEMPERATURE (°C) |
FINISH ROLLING TEMPERATURE (°C) |
COILING TEMPERATURE (°C) |
RETENTION TEMPERATURE (°C) |
RETENTION TIME (hr) |
COLLING RATE (°C/hr) |
131 |
A |
1096 |
870 |
511 |
764 |
54.5 |
10.2 |
INVENTIVE EXAMPLE |
132 |
B |
1097 |
886 |
479 |
768 |
18.7 |
0.4 |
COMPARATIVE EXAMPLE |
133 |
C |
1107 |
835 |
502 |
762 |
6.1 |
56.6 |
INVENTIVE EXAMPLE |
134 |
D |
1022 |
857 |
464 |
755 |
4.8 |
45.2 |
INVENTIVE EXAMPLE |
135 |
E |
1087 |
801 |
453 |
743 |
17.6 |
54.7 |
COMPARATIVE EXAMPLE |
136 |
F |
1069 |
858 |
576 |
761 |
34.0 |
49.8 |
INVENTIVE EXAMPLE |
137 |
G |
1032 |
931 |
444 |
738 |
35.9 |
16.5 |
COMPARATIVE EXAMPLE |
138 |
H |
1096 |
843 |
497 |
749 |
62.6 |
42.7 |
COMPARATIVE EXAMPLE |
139 |
I |
1046 |
895 |
536 |
754 |
48.1 |
24.5 |
INVENTIVE EXAMPLE |
140 |
Z |
1123 |
920 |
489 |
755 |
2.6 |
58.5 |
COMPARATIVE EXAMPLE |
141 |
AA |
1082 |
865 |
495 |
731 |
34.8 |
33.3 |
INVENTIVE EXAMPLE |
142 |
AB |
1058 |
924 |
482 |
749 |
26.5 |
24.3 |
INVENTIVE EXAMPLE |
143 |
AC |
1123 |
904 |
524 |
743 |
35.3 |
35.6 |
INVENTIVE EXAMPLE |
144 |
AD |
1077 |
877 |
498 |
741 |
10.4 |
0.8 |
COMPARATIVE EXAMPLE |
145 |
AE |
1008 |
939 |
574 |
753 |
22.1 |
28.7 |
INVENTIVE EXAMPLE |
146 |
AF |
1034 |
962 |
482 |
751 |
41.0 |
7.4 |
COMPARATIVE EXAMPLE |
147 |
AG |
1133 |
916 |
457 |
732 |
4.5 |
24.0 |
INVENTIVE EXAMPLE |
148 |
AH |
1037 |
884 |
561 |
748 |
59.0 |
9.4 |
INVENTIVE EXAMPLE |
149 |
AI |
979 |
847 |
508 |
752 |
59.9 |
4.6 |
COMPARATIVE EXAMPLE |
150 |
AJ |
1126 |
933 |
479 |
748 |
68.3 |
3.3 |
COMPARATIVE EXAMPLE |
151 |
AK |
1138 |
893 |
598 |
752 |
26.9 |
3.2 |
INVENTIVE EXAMPLE |
152 |
AL |
1063 |
865 |
584 |
746 |
40.3 |
2.6 |
INVENTIVE EXAMPLE |
[0078] Then, in the same manner as in the first experiment, the coefficient of micro-friction
of ferrite, and the spheroidized ratio and the average diameter of cementite of each
of the high-carbon steel sheets were measured, and further, the evaluation of adhesion
suppressive performance and the evaluation of crack sensitivity were performed. Results
of them are listed in Table 8 to Table 10. An underline in Table 8 to Table 10 indicates
that the item is out of the range of the present invention.
[Table 8]
SAMPLE No. |
COEFFICIENT OF MICRO-FRICTION OF FERRITE |
COEFFICIENT OF MICRO-FRICTION OF CEMENTITE |
SPHEROIDIZED RATIO OF CEMENTITE (%) |
AVERAGE DIAMETER OF CEMENTITE (µm) |
ADHESION SUPPRESSIVE PERFORMANCE |
CRACK SENSITIVITY |
REMARKS |
71 |
0.72 |
0.33 |
86.8 |
2.25 |
× |
× |
COMPARATIVE EXAMPLE |
72 |
0.43 |
0.31 |
87.9 |
1.15 |
○ |
○ |
INVENTIVE EXAMPLE |
73 |
0.64 |
0.27 |
78.3 |
0.63 |
× |
× |
COMPARATIVE EXAMPLE |
74 |
0.44 |
0.28 |
88.3 |
0.90 |
○ |
○ |
INVENTIVE EXAMPLE |
75 |
0.63 |
0.24 |
84.3 |
0.29 |
× |
× |
COMPARATIVE EXAMPLE |
76 |
0.59 |
0.24 |
90.3 |
0.42 |
× |
× |
COMPARATIVE EXAMPLE |
77 |
0.49 |
0.28 |
80.9 |
0.99 |
○ |
○ |
INVENTIVE EXAMPLE |
78 |
0.44 |
0.31 |
94.3 |
0.54 |
○ |
○ |
INVENTIVE EXAMPLE |
79 |
0.43 |
0.29 |
93.1 |
0.59 |
○ |
○ |
INVENTIVE EXAMPLE |
80 |
0.48 |
0.28 |
80.8 |
0.98 |
○ |
○ |
INVENTIVE EXAMPLE |
81 |
0.71 |
0.23 |
75.4 |
2.12 |
× |
× |
COMPARATIVE EXAMPLE |
82 |
0.44 |
0.22 |
87.1 |
0.65 |
○ |
○ |
INVENTIVE EXAMPLE |
83 |
0.47 |
0.34 |
82.0 |
1.25 |
○ |
○ |
INVENTIVE EXAMPLE |
84 |
0.61 |
0.34 |
62.3 |
1.04 |
× |
× |
COMPARATIVE EXAMPLE |
85 |
0.46 |
0.29 |
91.2 |
0.33 |
○ |
○ |
INVENTIVE EXAMPLE |
86 |
0.73 |
0.25 |
83.6 |
2.36 |
× |
× |
COMPARATIVE EXAMPLE |
87 |
0.64 |
0.23 |
98.9 |
1.16 |
× |
○ |
COMPARATIVE EXAMPLE |
88 |
0.47 |
0.30 |
93.0 |
0.92 |
○ |
○ |
INVENTIVE EXAMPLE |
89 |
0.45 |
0.28 |
94.8 |
0.63 |
○ |
○ |
INVENTIVE EXAMPLE |
90 |
0.45 |
0.27 |
97.1 |
0.43 |
○ |
○ |
INVENTIVE EXAMPLE |
91 |
0.44 |
0.32 |
96.5 |
0.68 |
○ |
○ |
INVENTIVE EXAMPLE |
92 |
0.45 |
0.28 |
90.4 |
0.46 |
○ |
○ |
INVENTIVE EXAMPLE |
[Table 9]
SAMPLE No. |
COEFFICIENT OF MICRO-FRICTION OF FERRITE |
COEFFICIENT OF MICRO-FRICTION OF CEMENTITE |
SPHEROIDIZED RATIO OF CEMENTITE (%) |
AVERAGE DIAMETER OF CEMENTITE (µm) |
ADHESION SUPPRESSIVE PERFORMANCE |
CRACK SENSITIVITY |
REMARKS |
101 |
0.72 |
0.31 |
82.3 |
0.77 |
× |
× |
COMPARATIVE EXAMPLE |
102 |
0.61 |
0.22 |
82.8 |
1.18 |
× |
○ |
COMPARATIVE EXAMPLE |
103 |
0.42 |
0.26 |
81.3 |
0.61 |
○ |
○ |
INVENTIVE EXAMPLE |
104 |
0.71 |
0.26 |
92.2 |
0.89 |
× |
○ |
COMPARATIVE EXAMPLE |
105 |
0.44 |
0.24 |
95.3 |
0.69 |
○ |
○ |
INVENTIVE EXAMPLE |
106 |
0.42 |
0.30 |
94.9 |
0.45 |
○ |
○ |
INVENTIVE EXAMPLE |
107 |
0.61 |
0.31 |
64.1 |
0.95 |
× |
× |
COMPARATIVE EXAMPLE |
108 |
0.43 |
0.32 |
95.4 |
0.53 |
○ |
○ |
INVENTIVE EXAMPLE |
109 |
0.42 |
0.26 |
89.8 |
0.56 |
○ |
○ |
INVENTIVE EXAMPLE |
110 |
0.44 |
0.34 |
88.0 |
1.01 |
○ |
○ |
INVENTIVE EXAMPLE |
111 |
0.44 |
0.34 |
84.2 |
2.07 |
○ |
○ |
INVENTIVE EXAMPLE |
112 |
0.69 |
0.25 |
89.6 |
0.63 |
× |
○ |
COMPARATIVE EXAMPLE |
113 |
0.59 |
0.32 |
85.5 |
1.29 |
× |
× |
COMPARATIVE EXAMPLE |
114 |
0.47 |
0.23 |
84.0 |
1.03 |
○ |
○ |
INVENTIVE EXAMPLE |
115 |
0.48 |
0.28 |
92.8 |
0.33 |
○ |
○ |
INVENTIVE EXAMPLE |
116 |
0.45 |
0.30 |
90.0 |
1.73 |
○ |
○ |
INVENTIVE EXAMPLE |
117 |
0.44 |
0.26 |
99.8 |
0.34 |
○ |
○ |
INVENTIVE EXAMPLE |
118 |
0.63 |
0.25 |
85.9 |
0.83 |
× |
× |
COMPARATIVE EXAMPLE |
119 |
0.47 |
0.23 |
93.9 |
0.66 |
○ |
○ |
INVENTIVE EXAMPLE |
120 |
0.45 |
0.28 |
95.9 |
0.41 |
○ |
○ |
INVENTIVE EXAMPLE |
121 |
0.46 |
0.24 |
87.9 |
0.65 |
○ |
○ |
INVENTIVE EXAMPLE |
122 |
0.39 |
0.25 |
80.6 |
0.43 |
○ |
○ |
INVENTIVE EXAMPLE |
[Table 10]
SAMPLE No. |
COEFFICIENT OF MICRO-FRICTION OF FERRITE |
COEFFICIENT OF MICRO FRICTION OF CEMENTITE |
SPHEROIDIZED RATIO OF CEMENTITE (%) |
AVERAGE DIAMETER OF CEMENTITE (µm) |
ADHESION SUPPRESSIVE PERFORMANCE |
CRACK SENSITIVITY |
REMARKS |
131 |
0.39 |
0.32 |
83.6 |
0.81 |
○ |
○ |
INVENTIVE EXAMPLE |
132 |
0.68 |
0.33 |
97.2 |
2.45 |
× |
× |
COMPARATIVE EXAMPLE |
133 |
0.40 |
0.24 |
89.9 |
0.63 |
○ |
○ |
INVENTIVE EXAMPLE |
134 |
0.40 |
0.24 |
87.2 |
0.86 |
○ |
○ |
INVENTIVE EXAMPLE |
135 |
0.66 |
0.31 |
88.1 |
0.74 |
× |
× |
COMPARATIVE EXAMPLE |
136 |
0.44 |
0.24 |
91.6 |
0.45 |
○ |
○ |
INVENTIVE EXAMPLE |
137 |
0.59 |
0.26 |
86.5 |
0.99 |
× |
○ |
COMPARATIVE EXAMPLE |
138 |
0.66 |
0.22 |
92.5 |
2.55 |
× |
× |
COMPARATIVE EXAMPLE |
139 |
0.38 |
0.32 |
97.5 |
0.59 |
○ |
○ |
INVENTIVE EXAMPLE |
140 |
0.60 |
0.22 |
82.7 |
0.22 |
× |
× |
COMPARATIVE EXAMPLE |
141 |
0.40 |
0.27 |
85.9 |
2.07 |
○ |
○ |
INVENTIVE EXAMPLE |
142 |
0.40 |
0.33 |
86.0 |
0.64 |
○ |
○ |
INVENTIVE EXAMPLE |
143 |
0.40 |
0.23 |
89.1 |
1.27 |
○ |
○ |
INVENTIVE EXAMPLE |
144 |
0.54 |
0.27 |
81.6 |
2.38 |
× |
× |
COMPARATIVE EXAMPLE |
145 |
0.43 |
0.31 |
93.5 |
0.33 |
○ |
○ |
INVENTIVE EXAMPLE |
146 |
0.62 |
0.24 |
82.4 |
1.77 |
× |
○ |
COMPARATIVE EXAMPLE |
147 |
0.37 |
0.31 |
81.0 |
0.30 |
○ |
○ |
INVENTIVE EXAMPLE |
148 |
0.40 |
0.32 |
90.4 |
0.93 |
○ |
○ |
INVENTIVE EXAMPLE |
149 |
0.72 |
0.33 |
94.5 |
0.68 |
× |
× |
COMPARATIVE EXAMPLE |
150 |
0.58 |
0.29 |
84.7 |
2.46 |
× |
× |
COMPARATIVE EXAMPLE |
151 |
0.43 |
0.23 |
94.5 |
0.67 |
○ |
○ |
INVENTIVE EXAMPLE |
152 |
0.44 |
0.25 |
80.4 |
0.46 |
○ |
○ |
INVENTIVE EXAMPLE |
[0079] As listed in Table 8, Samples No. 72, No. 74, No. 77 to No. 80, No. 82, No. 83, No.
85, and No. 88 to No. 92 were each within the range of the present invention, thus
being able to obtain good adhesion suppressive performance and crack sensitivity.
As listed in Table 9, Samples No. 103, No. 105, No. 106, No. 108 to No. 111, No. 114
to No. 117, and No. 119 to No. 122 were each also within the range of the present
invention, thus being able to obtain good adhesion suppressive performance and crack
sensitivity. As listed in Table 10, Samples No. 131, No. 133, No. 134, No. 136, No.
139, No. 141 to No. 143, No. 145, No. 147, No. 148, No. 151, and No. 152 were each
also within the range of the present invention, thus being able to obtain good adhesion
suppressive performance and crack sensitivity.
[0080] On the other hand, in Sample No. 71, the annealing retention temperature was too
high, and thus volume expansion was large, a hot-rolled coil was uncoiled to cause
abrasions, and a tightening mark caused by a tightening band also occurred. Further,
the thickness of the film of crystals of B greatly varied and the coefficient of micro-friction
of ferrite was large. Therefore, adhesion occurred. Further, cementite became coarse
excessively and a crack originating from the coarse cementite occurred during the
compression test. In Sample No. 73, the coiling temperature was too high, and thus
coarse lamellar pearlite was formed in the hot-rolled steel sheet, spheroidizing of
cementite during annealing was hindered, and the spheroidized ratio of cementite was
low. Further, large irregularities were formed with removal of scales and the coefficient
of micro-friction of ferrite was large. Therefore, adhesion and cracking during the
compression test occurred. In Sample No. 75, the annealing retention time was too
short, and thus the coefficient of micro-friction of ferrite was large and the average
diameter of cementite was small. Therefore, adhesion and cracking during the compression
test occurred. In Sample No. 76, the slab heating temperature was too low, and thus
segregations of B, Mn, and others were not eliminated and the coefficient of micro-friction
of ferrite was large. Therefore, adhesion and cracking during the compression test
occurred. In Sample No. 81, the coiling temperature was too high, and thus adhesion
and cracking during the compression test occurred similarly to Sample No. 73. In Sample
No. 84, the cooling rate was too high, and thus pearlite transformation occurred during
cooling and a crack originating from acicular cementite occurred during the compression
test. Further, a good film of crystals of B was not formed on the surface of the high-carbon
steel sheet, the coefficient of micro-friction of ferrite was high, and adhesion occurred.
In Sample No. 86, the annealing retention temperature was too high, and thus adhesion
and cracking during the compression test occurred, similarly to Sample No. 81. In
Sample No. 87, the coiling temperature was too low, and thus as a result of removal
of scales, the surface of the steel sheet became rough and adhesion occurred.
[0081] In Sample No. 101, the annealing retention temperature was too low, and thus the
segregation of B to the interface between ferrite and austenite was suppressed, the
coefficient of micro-friction of ferrite was large, and adhesion occurred. Further,
the segregation of B to the interface between ferrite and cementite was also suppressed
and cracking occurred during the compression test. In Sample No. 102, the finish rolling
temperature was too high, and thus large irregularities were formed with removal of
scales and the coefficient of micro-friction of ferrite was large. Therefore, adhesion
occurred. In Sample No. 104, the slab heating temperature was too high, and thus B
atoms were oxidized during slab heating and the coefficient of micro-friction of ferrite
was large. Therefore, adhesion occurred. In Sample No. 107, the cooling rate was too
high, and thus pearlite transformation occurred during cooling and a crack originating
from acicular cementite occurred during the compression test. Further, a good film
of crystals of B was not formed on the surface of the high-carbon steel sheet, the
coefficient of micro-friction of ferrite was high, and adhesion occurred. In Sample
No. 112, the slab heating temperature was too high, and thus adhesion occurred, similarly
to Sample No. 104. In Sample No. 113, the finish rolling temperature was too low,
and thus anisotropy of the structure was strong and a crack originating from a nonuniform
structure occurred during the compression test. Further, as a result of removal of
scales, the surface of the steel sheet became rough and adhesion occurred. In Sample
No. 118, the annealing retention temperature was too low, and thus adhesion and cracking
during the compression test occurred, similarly to Sample No. 101.
[0082] In Sample No. 132, the cooling rate was too low, and thus the thickness of the film
of crystals of B greatly varied and the coefficient of micro-friction of ferrite was
large. Therefore, adhesion occurred. Further, cementite became coarse excessively
and a crack originating from the coarse cementite occurred during the compression
test. In Sample No. 135, the finish rolling temperature was too low, and thus anisotropy
of the structure was strong and a crack originating from a nonuniform structure occurred
during the compression test. Further, as a result of removal of scales, the surface
of the steel sheet became rough and adhesion occurred. In Sample No. 137, the coiling
temperature was too low, and thus as a result of removal of scales, the surface of
the steel sheet became rough and adhesion occurred. In Sample No. 138, the annealing
retention time was too long, and thus volume expansion was large, a hot-rolled coil
was uncoiled to cause abrasions, and a tightening mark caused by a tightening band
also occurred. Further, the thickness of the film of crystals of B greatly varied
and the coefficient of micro-friction of ferrite was large. Therefore, adhesion occurred.
Further, cementite became coarse excessively and a crack originating from the coarse
cementite occurred during the compression test. In Sample No. 140, the annealing retention
time was too short, and thus the coefficient of micro-friction of ferrite was large
and the average diameter of cementite was small. Therefore, adhesion and cracking
during the compression test occurred. In Sample No. 144, the cooling rate was too
low, and thus adhesion and cracking during the compression test occurred, similarly
to Sample No. 132. In Sample No. 146, the finish rolling temperature was too high,
and thus, large irregularities were formed with removal of scales and the coefficient
of micro-friction of ferrite was large. Therefore, adhesion occurred. In Sample No.
149, the slab heating temperature was too low, and thus segregations of B, Mn, and
others were not eliminated and the coefficient of micro-friction of ferrite was large.
Therefore, adhesion and cracking during the compression test occurred. In Sample No.
150, the annealing retention time was too long, and thus adhesion and cracking during
the compression test occurred, similarly to Sample No. 138.
[0083] Fig. 7 illustrates the relationship between the coefficient of micro-friction of
ferrite and the B content in the samples out of the examples in the first experiment
or third experiment. As illustrated in Fig. 7, when the B content is 0.0008% or more,
the coefficient of micro-friction of ferrite is much lower as compared to the case
when it is less than 0.0008%.
INDUSTRIAL APPLICABILITY
[0084] The present invention may be utilized in, for example, manufacturing industries and
application industries of high-carbon steel sheets used for various steel products,
such as a driving system component for automobile, a saw, a knife, and others.