JP4501699B2 - High-strength steel sheet excellent in deep drawability and stretch flangeability and method for producing the same - Google Patents

Description

  The present invention has a high tensile strength (TS) of 440 MPa or more, a hole expansion ratio λ ≧ 80%, and a Rankford value (r value) ≧ 1.2, which is useful for applications such as automobiles and electrical devices. The present invention intends to propose a high-strength steel sheet excellent in both stretch flangeability and deep drawability and a method for producing the same.

  Steel sheets used by press forming in industrial fields such as automobiles, electrical equipment, and machines are required to have both excellent strength and ductility, and such required characteristics are increasing more and more in recent years.

For example, in the field of the automobile industry, in recent years, in order to regulate CO ₂ emissions from the viewpoint of global environmental conservation, there has been a demand for improving the fuel efficiency of automobiles. In addition, in order to ensure the safety of passengers in the event of a collision, it is also required to improve safety centered on the collision characteristics of the automobile body. Thus, both weight reduction and reinforcement of the automobile body are being actively promoted.

  In order to satisfy the weight reduction and strengthening of automobile bodies at the same time, it is said that it is effective to increase the strength of component materials within a range where rigidity does not matter, and to reduce the weight by reducing the plate thickness. Steel plates are actively used in automotive parts. Since the weight reduction effect increases as the strength of the steel sheet used increases, in the automobile industry, for example, a steel sheet having a tensile strength (TS) of 440 MPa or more is used as a panel material for inner plates and outer plates.

  On the other hand, since many automobile parts made of steel plates are formed by press working, the steel plates for automobiles are required to have excellent press formability. However, the high-strength steel sheet is greatly deteriorated in formability as compared with a normal mild steel sheet. Therefore, TS ≧ 440 MPa, more preferably TS ≧ 500 MPa, more preferably TS ≧ There is an increasing demand for a steel plate having not only ductility (El) but also good stretch flangeability and deep drawability for a part shape that is 590 MPa and becomes more complex year by year.

Conventionally, as a steel sheet having both strength (TS) and ductility (El), a composite structure steel sheet (Dual Phase steel sheet, DP steel sheet) having a composite structure of a ferrite phase and a martensite phase is known (for example, a patent). Literature 1 etc.). The steel sheet not only has good ductility, but also has a good shape freezing property during processing because of low yield stress, and by controlling the structure, a steel sheet having high TS and excellent El can be obtained. It was inferior in stretch flangeability (local ductility) and deep drawability.
JP-A-55-122820

  Therefore, in order to cope with complicated press-formed parts, while maintaining the low yield ratio and good TS-El balance, which are the features of DP steel sheets, the low stretch flangeability and low depth that were the disadvantages of the DP steel sheets are included. There is an urgent need to provide a high-strength composite steel sheet that overcomes the drawability and is excellent in both.

Conventionally, in order to increase the r value of cold-rolled steel sheets, it is desirable to reduce solute C and N as much as possible in the hot-rolled sheet stage, and carbonitride-forming elements such as Ti and Nb are added to ultra-low carbon steel The so-called IF (Interstitial atom free) steel has been used as a base, and the strength has been increased by adding a solid solution strengthening element such as Si, Mn, and P to the steel (for example, Patent Document 2).
JP-A-56-139654

On the other hand, as a method for improving stretch flangeability of a composite structure steel sheet, in Patent Document 3, tempered martensite and tempered bainite are essential for the parent phase, and a martensite phase with an occupation ratio of 3 to 30% is defined as the second phase. Although the stretch flangeability of the composite structure steel sheet is improved by using the composite structure steel sheet, {111} recrystallization is performed with annealing in the presence of sufficient solid solution C to obtain the martensite phase. There is no technical idea for increasing the r-value by developing the texture. In addition, the fact that the tempering process is indispensable places a burden on the process, equipment, and cost.
Japanese Patent Laid-Open No. 2003-247045

Moreover, in patent document 4, with the composite structure steel plate which consists of a ferrite phase and a martensite phase, favorable stretch flangeability ((lambda)> = 50%) is obtained by prescribing | regulating the area ratio of a martensite and its particle size. . However, although the case where at least one selected from Nb, Ti and V is added as a carbonitride-forming element with respect to C: 0.06 to 0.21% by mass is disclosed, the reason for the addition is the mechanical strength of the steel sheet, This is especially for increasing the yield point. From the addition amount, there is no concept of IF, and there is no technical idea for developing a {111} recrystallized texture, so a high r value cannot be obtained.
JP 2003-213369 A

As an attempt to improve the r value of such a composite structure steel plate, for example, there is a technique of Patent Document 5 or Patent Document 6.
Japanese Patent Publication No.55-10650 JP-A-55-100934

Patent Document 5 discloses a method in which after cold rolling, box annealing is performed at a temperature of a recrystallization temperature to an Ac ₃ transformation point, and then heating to 700 to 800 ° C. is performed for quenching and tempering to obtain a composite structure. It is disclosed. However, in this method, since the quenching and tempering is performed during the continuous annealing, the manufacturing cost becomes a problem. Further, box annealing is inferior in terms of processing time and efficiency as compared to continuous annealing.

  In the technique of Patent Document 6, after cold rolling in order to obtain a high r value, box annealing is first performed, and the temperature at this time is set to a two-phase region of a ferrite (α) phase and an austenite (γ) phase, and then continuously. Annealing is performed. In this technique, Mn is concentrated from the α phase to the γ phase during soaking of the box annealing. This Mn-concentrated phase preferentially becomes a γ phase during the subsequent continuous annealing, and a mixed structure can be obtained even at a cooling rate of the order of a gas jet. However, this method requires a relatively high temperature and long-time box annealing to concentrate Mn, and therefore, in the manufacturing process, such as frequent adhesion between steel plates, generation of temper collar, and decrease in the life of the furnace inner cover. There are many problems.

Patent Document 7 discloses that C: 0.003 to 0.03%, Si: 0.2 to 1%, Mn: 0.3 to 1.5%, Ti: 0.02 to 0.2% (however, (effective Ti) / (C + N) atomic concentration ratio) 0.4 to 0.8), which is hot-rolled, cold-rolled, and then subjected to continuous annealing that is rapidly cooled after heating to a predetermined temperature, and is a composite structure type excellent in deep drawability and shape freezeability Although a method for producing high-tensile cold-rolled steel sheets has been disclosed, water quenching equipment is required to obtain a high cooling rate of 100 ° C / s, and water-quenched steel sheets have problems with surface treatment properties. Therefore, there are problems in manufacturing equipment and materials.
Japanese Patent Publication No. 1-35900

Furthermore, Patent Document 8 discloses a technique for improving the r value of a composite structure steel sheet by optimizing the V content in relation to the C content. This is because by precipitating C in the steel as V-type carbides before recrystallization annealing to reduce the amount of dissolved C as much as possible to achieve a high r value, and subsequently heating in the two-phase region of α-γ, V-type carbides are dissolved to concentrate C in γ, and a martensite phase is generated in the subsequent cooling process. However, the addition of V causes an increase in cost because it is expensive, and further, VC precipitated in the hot-rolled sheet increases the deformation resistance during cold rolling, so that the reduction rate in the example is 70%. Cold rolling has a manufacturing problem such as an increased load on the roll, increasing the risk of occurrence of trouble, and concern about a decrease in productivity.
Japanese Patent Laid-Open No. 2002-226941

Moreover, there exists a technique of patent document 9 as a technique of the high strength steel plate excellent in deep drawability, and its manufacturing method. This technique obtains a high-strength steel sheet containing a predetermined amount of C, having an average r value of 1.3 or more, and having a total of 3% or more of one or more of a bainite phase, a martensite phase and an austenite phase in the structure. Yes, the manufacturing method is 30% to 95% reduction in cold rolling, and then annealing to increase the r value by developing the texture by forming Al and N clusters and precipitates, The structure is characterized in that a heat treatment is performed so as to have at least 3% of at least one of a bainite phase, a martensite phase, and an austenite phase in the structure. In this method, after cold rolling, annealing for obtaining a good r value and heat treatment for forming a structure are required, and in the annealing process, the holding time is a long time of 1 hour or more. There is a problem that productivity is poor in terms of process (time). Furthermore, since the second phase fraction of the obtained structure is relatively high, it is difficult to stably secure an excellent strength ductility balance.
JP 2003-64444 A

  Patent Documents 5 to 9 described above all improve the deep drawability and are not a technique for improving stretch flangeability, but a technique for improving deep drawability and improving stretch flangeability has been demanded.

  In order to increase the strength of a (soft) steel sheet having excellent deep drawability, the conventional methods for increasing the strength by solid solution strengthening require the addition of a large amount or an excess of alloy components, In terms of process, process, and improvement of the r value itself have been problematic.

  In addition, the conventionally studied methods for improving the stretch flangeability of a composite steel sheet have no technical idea of increasing the r value by developing a {111} recrystallized texture, and the stretch flangeability and deep drawability are improved. It was not something that made them compatible.

  An object of the present invention is to propose a high-strength steel sheet excellent in stretch flangeability and deep drawability and a method for producing the same, which advantageously solves the problems of the prior art.

  The present invention has been intensively studied to solve the above-mentioned problems. As a result, the C content is within the range of 0.010 to 0.050% by mass without using any special or excessive alloy components or equipment. By regulating the Nb content in relation to the amount, (a) the {111} recrystallized texture is developed, the average r value is 1.2 or more, and the deep drawability is excellent; and (b) the ferrite phase and martensite (C) High strength with excellent stretch flangeability by optimizing the area fraction of the martensite phase and the hardness of the second phase including the martensite phase while having a steel structure containing the phase Successfully obtained a steel plate.

First, basic experimental results performed by the present inventors will be described.
Various steel materials with the basic component in the range of 0.025 to 0.08% C-0.5% Si-2.0% Mn-0.035% P-0.005% S-0.03% Al-0.002% N-0 to 0.5% Nb After heating to 1250 ° C. and maintaining soaking at this temperature, hot rolling was performed so that the finish rolling finish temperature was 860 ° C., and the plate thickness was 3 mm. Furthermore, after finishing rolling, a heat retention treatment was performed at 650 ° C. for 3 hours as a coil winding equivalent treatment, pickling, and then cold rolling at a reduction rate of 60% to a plate thickness of 1.2 mm. Next, after cooling these cold-rolled plates to a maximum temperature of 850 ° C (annealing temperature), the temperature range from 800 ° C to 300 ° C as an average cooling rate of 15 ° C / s, and holding at 300 ° C for 120 seconds Then, continuous annealing for cooling to room temperature was performed.

The obtained cold-rolled annealed sheet was examined for the microstructure, hardness measurement, hole expansion rate (λ value) and r value.
The survey method is as follows.

(I) Microstructure of cold-rolled annealed plates Test specimens were taken from each cold-rolled annealed plate, and the microstructure (L section) parallel to the rolling direction was measured using an optical microscope or a scanning electron microscope. Was observed.

(Ii) Hardness measurement A test piece was taken from each of the obtained cold-rolled annealed plates, and the hardness of the ferrite phase and the hardness of the second phase were measured. In addition, the size of the second phase of the steel of the present invention is fine, and although it is not impossible to measure with a micro Vickers hardness meter that has been conventionally used for measuring the hardness of a minute region, there is a large variation and there is a problem in accuracy. Therefore, measurement was performed with a nano hardness tester capable of measuring hardness even when the size was 1 μm or less.
For the nano hardness, after grinding from the steel plate surface to 1/4 thickness and removing the grinding strain by electropolishing, measure the hardness of ferrite phase and second phase using 30 TRIBOSCOPEs from Hysitron. The average value was taken as the hardness value. The measurement was performed with substantially the same indentation size. Specifically, the hardness was measured by adjusting the load so that the indentation depth (= contact depth) proportional to the size of the indentation was 50 ± 10 nm.

(Iii) λ value (stretch flangeability)
A test piece of 100 mm square was taken from each of the obtained cold-rolled annealed plates and subjected to a hole expansion test in accordance with the provisions of the Japan Iron and Steel Federation Standard JFST 1001. In other words, a punch hole punched out with a 10mmφ punch is opened on the specimen, and a conical punch with an apex angle of 60 ° is used so that the burr is on the outside, and the hole is expanded until a crack that penetrates the plate thickness occurs. D ₀ : initial hole inner diameter (mm), d: hole inner diameter (mm) when cracking occurred, hole expansion ratio λ (%) = {(d−d ₀ ) / d ₀ } × 100 .

(Vi) r value (deep drawability)
JIS No. 5 tensile test specimens were collected from the rolling direction (L direction) of each obtained cold-rolled annealed plate, 45 ° direction (D direction) with respect to the rolling direction, and 90 ° direction (C direction) with respect to the rolling direction. Measure the width strain and plate thickness strain of each specimen when 10% uniaxial tensile strain was applied to these specimens, and use these measurements to determine the average r value in accordance with JIS Z 2254 regulations. (Average plastic strain ratio) was calculated and used as the r value.

  FIG. 1 shows the relationship between the Nb content ([Nb]) and the C content ([C]) in steel sheets containing various C contents, that is, ([Nb] / 93) / ([C] / 12) shows an influence on the hardness ratio, the λ value and the average r value.

  From FIG. 1, it is assumed that C is a relatively low C content of 0.025% and ([Nb] / 93) / ([C] / 12) = 0.2 to 0.7, that is, the Nb content is C By limiting the atomic ratio to the content to be Nb / C = 0.2 to 0.7, a ferrite phase and a second phase including a martensite phase having a hardness 1.5 to 3 times that of the ferrite phase are obtained. It has been clarified that a cold rolled steel sheet having a composite structure and having a high λ value and a high r value can be produced.

The present invention has been completed by further study based on the above-described findings, and the gist thereof is as follows.
(I) By mass%
C: 0.010 to 0.050%
Si: 1.0% or less,
Mn: 1.0-3.0%
P: 0.005-0.1%
S: 0.01% or less,
Al: 0.005-0.5%
N: 0.01% or less and
Nb: 0.01-0.3%
And the following formulas (1), (2) and (3) are satisfied, the balance has a component composition consisting of Fe and inevitable impurities, and consists of a ferrite phase and a second phase as main phases, The ratio H (S) / H (F) of the hardness H (S) of the second phase to the hardness H (F) of the ferrite phase is in the range of 1.5 to 3.0, and the area ratio of the ferrite phase to the entire structure is 50%. A high-strength steel sheet excellent in deep drawability and stretch flangeability, characterized in that the second phase has a steel structure containing a martensite phase in an area ratio of 1 to 15% with respect to the entire structure.
Record
0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (1)
3-100 × [C] ≦ Mn equivalent (%) ≦ 7-100 × [C] (2)
Mn equivalent (%) = [Mn] (3)
However, [Nb], [C] and [Mn] in the formula are the contents (mass%) of each element.

(II) By mass%
C: 0.010 to 0.050%
Si: 1.0% or less,
Mn: 1.0-3.0%
P: 0.005-0.1%
S: 0.01% or less,
Al: 0.005-0.5%
N: 0.01% or less and
Nb: 0.01-0.3%
In addition, one or more of Mo, Cr, Cu and Ni is contained in a total of 0.5% or less, and the following formulas (1), (2) and (4) are satisfied, and the balance is It has a component composition consisting of Fe and inevitable impurities, and consists of a ferrite phase and a second phase, which are the main phases. The ratio of the hardness H (S) of the second phase to the hardness H (F) of the ferrite phase H (S) / H (F) is in the range of 1.5 to 3.0, the area ratio of the ferrite phase to the entire structure is 50% or more, and the martensite is 1 to 15% in the area ratio of the entire structure in the second phase. A high-strength steel sheet excellent in deep drawability and stretch flangeability, characterized by having a steel structure containing a phase.
Record
0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (1)
3-100 × [C] ≦ Mn equivalent (%) ≦ 7-100 × [C] (2)
Mn equivalent (%) = [Mn] + 3.3 x [Mo] + 1.3 x [Cr] + 0.5 x [Cu] + 0.4 x [Ni] (4)
However, [Nb], [C], [Mn], [Mo], [Cr], [Cu] and [Ni] in the formula are the contents (mass%) of each element.

(III) In addition to the above composition, further containing Ti: 0.1% by mass or less, satisfying the following formula (5), and based on the effective Ti amount [Ti ^* ] represented by the following formula (6) In addition to the above formula (1), it satisfies the following formula (7) or the following formula (8), and is excellent in deep drawability and stretch flangeability as described in the above (I) or (II) High strength steel plate.
([Ti] / 48) / {([S] / 32) + ([N] / 14)} ≦ 2.0 (5)
[Ti ^* ] = [Ti] −48 × {([N] / 14) + ([S] / 32)} (6)
[Ti ^* ]> 0, 0.2 ≦ {([Nb] / 93) + ([Ti ^* ] / 48)} / ([C] / 12) ≦ 0.7 · (7)
[Ti ^* ] ≦ 0, 0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (8)
However, [Ti], [S], [N], [Nb], and [C] in the formula are the contents (mass%) of each element.

 (IV) The high-strength steel sheet excellent in deep drawability and stretch flangeability according to any one of (I) to (III) above, wherein the surface has a plating layer.

(V) By mass%
C: 0.010 to 0.050%
Si: 1.0% or less,
Mn: 1.0-3.0%
P: 0.005-0.1%
S: 0.01% or less,
Al: 0.005-0.5%
N: 0.01% or less and
Nb: 0.01-0.3%
Contain, and the following (1), (2) and (3) meets the equation, balance finishing a steel slab having a composition consisting of Fe and unavoidable impurities by hot rolling rolling delivery temperature: 800 A finish rolling is performed at a temperature of ℃ or higher, a coiling temperature is wound at 400 to 720 ℃, a hot rolling step to be a hot rolled sheet, and the hot rolled sheet is subjected to a cold rolling at a rolling reduction of 40% or more, Cold rolling process for forming a cold-rolled sheet, and annealing the cold-rolled sheet at an annealing temperature of 800 to 950 ° C, and then from 800 ° C to a temperature in the temperature range of 400 to 200 ° C, an average cooling rate: 5 ° C A method for producing a high-strength steel sheet excellent in deep drawability and stretch flangeability, characterized by sequentially performing a cold-rolled sheet annealing step of cooling at / s or higher, and then cooling after holding at the temperature for 1 second or longer.
Record
0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (1)
3-100 × [C] ≦ Mn equivalent (%) ≦ 7-100 × [C] (2)
Mn equivalent (%) = [Mn] (3)
However, [Nb], [C] and [Mn] in the formula are the contents (mass%) of each element.

(VI) By mass%
C: 0.010 to 0.050%
Si: 1.0% or less,
Mn: 1.0-3.0%
P: 0.005-0.1%
S: 0.01% or less,
Al: 0.005-0.5%
N: 0.01% or less and
Nb: 0.01-0.3%
Contains further Mo, Cr, containing 0.5% in total of one or more of Cu and Ni, and the following (1), meets the (2) and (4), the balance Is a steel slab having a composition composed of Fe and inevitable impurities , hot-rolled to finish rolling to a finish rolling exit temperature of 800 ° C or higher, wound at a winding temperature of 400 to 720 ° C, and hot rolled A cold rolling step in which the hot-rolled sheet is cold-rolled at a rolling reduction of 40% or more to obtain a cold-rolled sheet, and the cold-rolled sheet is annealed at a temperature of 800 to 950 ° C. A cold-rolled sheet annealing step in which annealing is performed, and then cooling is performed at an average cooling rate of 5 ° C./s or higher from 800 ° C. to a temperature range of 400 to 200 ° C. A method for producing a high-strength steel sheet excellent in deep drawability and stretch flangeability, characterized by sequentially applying.
Record
0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (1)
3-100 × [C] ≦ Mn equivalent (%) ≦ 7-100 × [C] (2)
Mn equivalent (%) = [Mn] + 3.3 x [Mo] + 1.3 x [Cr] + 0.5 x [Cu] + 0.4 x [Ni] (4)
However, [Nb], [C], [Mn], [Mo], [Cr], [Cu] and [Ni] in the formula are the contents (mass%) of each element.

(VII) In addition to the above composition, further containing Ti: 0.1% by mass or less, satisfying the following formula (5), and based on the effective Ti amount [Ti ^* ] represented by the following formula (6) In addition to the above formula (1), it satisfies the following formula (7) or the following formula (8), and is excellent in deep drawability and stretch flangeability as described in the above (V) or (VI) Manufacturing method of high strength steel sheet.
([Ti] / 48) / {([S] / 32) + ([N] / 14)} ≦ 2.0 (5)
[Ti ^* ] = [Ti] −48 × {([N] / 14) + ([S] / 32)} (6)
[Ti ^* ]> 0, 0.2 ≦ {([Nb] / 93) + ([Ti ^* ] / 48)} / ([C] / 12) ≦ 0.7 (7)
[Ti ^* ] ≤0, 0.2≤ ([Nb] / 93) / ([C] / 12) ≤0.7 (8)
However, [Ti], [S], [N], [Nb], and [C] in the formula are the contents (mass%) of each element.

 (VIII) The deep drawability according to any one of (V) to (VII) above, further comprising a plating treatment step of forming a plating layer on the surface of the steel sheet after the cold rolled sheet annealing step. And a method for producing high-strength steel sheets with excellent stretch flangeability.

  This invention is necessary for the formation of martensite when the C content is in the range of 0.010 to 0.050% by mass without thorough reduction of the solid solution C that adversely affects the deep drawability as in the conventional ultra-low carbon IF steel. Despite the state in which a certain amount of solute C remains, the {111} recrystallized texture is developed to secure an average r value ≧ 1.2 and have good deep drawability, and the steel structure is mainly used. Having a ferrite phase which is a phase and a second phase having a hardness ratio between the ferrite phase of 1.5 and 3.0, and the second phase having a martensite phase, the hole expansion ratio λ ≧ 80 %, TS440 MPa or higher, more preferably TS500 MPa or higher, even more preferably TS590 MPa or higher.

Although the reason for this is not necessarily clear, it can be considered as follows.
In order to increase the r value, that is, to develop the {111} recrystallization texture, in conventional mild steel sheets, the solute C before cold rolling and recrystallization is reduced as much as possible, and the hot rolled sheet structure is refined. To do so has been an effective means. On the other hand, in the DP steel sheet as described above, since solute C necessary for the formation of the martensite phase is required, the recrystallization texture of the parent phase does not develop and the r value is low.

  However, in the present invention, it is newly found that there is an exquisite proper component range that enables both {111} recrystallization texture development and martensite phase formation. The martensite phase obtained depending on the conditions is smaller and finer than the martensite phase of conventional DP steel, and contributes to reducing the hardness ratio to the ferrite phase (the hardness of the martensite phase is in γ High λ value as well as high r value is achieved.

  That is, the C content is 0.010 to 0.050% by mass, in which the amount of C is higher than that of extremely low carbon steel while reducing the amount of C compared to the conventional DP steel sheet (low carbon steel level). By adding Nb appropriately according to the amount, it is possible to simultaneously achieve both {111} recrystallization texture development and the formation of the second phase including the optimal martensite phase that can obtain a high λ value. I found it.

  As conventionally known, since Nb has a recrystallization delay effect, it is possible to refine the hot-rolled sheet structure by appropriately controlling the finishing temperature during hot rolling. Nb has a high carbide forming ability.

  In the present invention, in particular, the hot rolling finish temperature is set to an appropriate range immediately above the transformation point, and in addition to refining the hot rolled sheet structure, the coil winding temperature after hot rolling is also set appropriately so that hot rolling NbC is precipitated in the plate to reduce solid solution C before cold rolling and before recrystallization.

  Here, by setting the Nb content and the C content to satisfy 0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7, there is an intentional presence of C that does not precipitate as NbC. The present invention has originality.

  Conventionally, the presence of such C has been considered to inhibit the development of {111} recrystallized texture, but in the present invention, the total C content is not precipitated and fixed as NbC, and is necessary for the formation of the martensite phase. A high r value can be achieved while solid solution C is present.

  Furthermore, the martensite phase produced by this appropriate amount of solute C and an appropriate manufacturing method contributes to improving the stretch flangeability of the composite structure steel in terms of quantity and quality, and also has a high λ value. Can be achieved.

  The reason for this is not clear, but first, for increasing the r value, in addition to the refinement of the hot-rolled sheet structure, in addition to the negative factor for the formation of {111} recrystallized texture due to the presence of solute C, It is thought that the positive factor of precipitating fine NbC to accumulate strain near the grain boundary during cold rolling and promote the generation of {111} recrystallized grains from the grain boundary is greater. In particular, the effect of precipitating NbC in the matrix is not effective at the C content of the conventional ultra-low carbon steel, and is the first effect in the proper range of C content of the present invention (0.010 to 0.050 mass%). It is presumed that this is exhibited, and finding the appropriate range of the C content is the basis of the technical idea of the present invention.

  And, it is presumed that C other than NbC and its existence form are probably cementite-based carbides or solid solution C. However, due to the presence of C that is not fixed as NbC, the martensite phase is reduced during cooling in the annealing process. At the same time as forming and succeeding in increasing strength, the martensite phase obtained at that time is finely dispersed in the second phase in a small amount compared to conventional DP steel, and this is compared with the ferrite phase of the parent phase. It is thought that the hole expandability was improved because the hardness ratio of the surrounding second phase was reduced.

  In addition, by limiting the Mn equivalent (%) to satisfy the relationship of 3-100 × [C] ≦ Mn equivalent (%) in relation to the C content, hardness effective for strengthening the structure can be obtained. And an excessively hard martensite phase that deteriorates stretch flangeability by limiting to satisfy the relationship of Mn equivalent (%) ≦ 7−100 × [C]. As a result, the hole expansibility is further improved.

  In addition, the manufacturing method of the present invention, in particular, cools at an average cooling rate of 5 ° C./s or more from 800 ° C. to a temperature in the temperature range of 400 to 200 ° C. after annealing, and then holds at that temperature for 1 second or more. Thus, although details are not clear, the formation of a so-called low-temperature transformation phase such as a martensite phase having a low internal stress or a low-temperature bainite phase is promoted, and as a result, hole expansibility is remarkably improved.

  According to the production method of the present invention, in order to increase the r value relative to the prior art, in the steelmaking process, a degassing step for making an ultra-low carbon steel is unnecessary, and because the structure strengthening is used, There is no need to add excessive alloying elements that rely on solid solution strengthening, which can be adequately handled by existing equipment and is advantageous in terms of cost, as well as strength ductility balance, stretch flangeability and deep drawability. Thus, it is possible to produce a steel sheet having improved formability, which is improved in formability, which has been regarded as a drawback of the conventional composite structure steel sheet.

The present invention is described in detail below.
In addition, although the unit of content of the element in steel is all “mass%”, hereinafter, it is simply indicated by “%” unless otherwise specified.
First, the reason for limiting the component composition of the high-strength steel sheet of the present invention will be described.

C: 0.010 to 0.050%
C is an important element in the present invention together with Nb described later. C is effective for increasing the strength and promotes the formation of a composite structure having a ferrite phase as a main phase and a second phase including a martensite phase. Therefore, in the present invention, C is 0.010% or more from the viewpoint of forming a composite structure. It is necessary to contain. Preferably, it is 0.015% or more. On the other hand, if C content exceeds 0.050%, a high λ value and a high r value cannot be obtained, so the upper limit of the C content is 0.050%.

Si: 1.0% or less
Si promotes ferrite transformation and increases the C content in untransformed austenite to facilitate the formation of a composite structure of ferrite phase and martensite phase, and has an effect of strengthening solid solution. In order to acquire the said effect, it is preferable to contain Si 0.01% or more, More preferably, it is 0.05% or more. However, if Si exceeds 1.0%, a surface defect called red scale occurs during hot rolling, so the surface appearance of the steel sheet is deteriorated, so the upper limit of Si content is 1.0%. To do.
In addition, when hot dip galvanizing is performed, the wettability of the plating is deteriorated to cause uneven plating and the plating quality is deteriorated. Therefore, the Si content is preferably reduced and should be 0.7% or less. desirable.

Mn: 1.0-3.0%
Mn is effective in increasing strength and has the effect of slowing down the critical cooling rate at which a martensite phase is obtained, and promotes the formation of the martensite phase during cooling after annealing, so the required strength level and after annealing The Mn is preferably an element effective for preventing hot cracking due to S. From such a viewpoint, Mn needs to be contained at 1.0% or more, preferably 1.2% or more. On the other hand, containing excessive Mn exceeding 3.0% degrades the r value and weldability, so the upper limit of the Mn content is 3.0%.

P: 0.005-0.1%
P is an element having an effect of solid solution strengthening. However, if the P content is less than 0.005%, not only the effect does not appear, but also the dephosphorization cost increases in the steel making process. Therefore, P is contained in an amount of 0.005% or more, preferably 0.01% or more. On the other hand, if the P content exceeds 0.1%, P segregates at the grain boundaries, and the secondary work brittleness resistance and weldability deteriorate. Moreover, when it is set as the hot dip galvanized steel sheet, the diffusion of Fe from the steel sheet to the plated layer at the interface between the plated layer and the steel sheet is suppressed during the alloying process after the hot dip galvanizing, and the alloying processability is deteriorated. For this reason, an alloying treatment at a high temperature is required, and the obtained plating layer is likely to undergo plating peeling such as powdering and chipping. Therefore, the upper limit of the P content is set to 0.1%.

S: 0.01% or less S is an impurity and causes hot cracking, and also exists as inclusions in steel and deteriorates various properties of the steel sheet, so it is necessary to reduce it as much as possible. Specifically, the S content is 0.01% or less because it is acceptable up to 0.01%.

Al: 0.005-0.5%
In addition to being useful as a deoxidizing element for steel, Al has the effect of fixing solute N present as an impurity and improving the normal temperature aging resistance. Furthermore, Al is useful as a temperature adjusting component in the α-γ2 phase region as a ferrite-forming element. In order to exert such an effect, the Al content needs to be 0.005% or more. On the other hand, the content of Al exceeding 0.5% causes high alloy costs and further induces surface defects, so the upper limit of Al content is set to 0.5%. More preferably, it is 0.1% or less.

N: 0.01% or less N is an impurity and is an element that deteriorates room temperature aging resistance. It is an element that is preferably reduced as much as possible. When the N content increases, the room temperature aging resistance deteriorates, and a large amount of Al or Ti is required to fix the solid solution N, but up to 0.01% is acceptable, so the upper limit of the N content is 0.01%. %.

Nb: 0.01 to 0.3% and 0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7
Nb is the most important element in the present invention, and has the effect of refining the hot-rolled sheet structure and precipitating and fixing C as NbC in the hot-rolled sheet, and contributes to increasing the r value. From such a viewpoint, Nb needs to be contained in an amount of 0.01% or more. On the other hand, in the present invention, solid solution C is required for forming a martensite phase having an appropriate hardness in the cooling process after annealing, but excessive Nb content exceeding 0.3% prevents this formation. Therefore, the upper limit of Nb content is 0.3%.

  In order to achieve the effect of Nb content, the Nb content (% by mass) and the C content (% by mass) are preferably 0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (however, In the formula, [Nb] and [C] must contain Nb and C so as to satisfy the range of the content (mass%) of each element. Here, ([Nb] / 93) / ([C] / 12) represents the atomic concentration ratio of Nb and C. If ([Nb] / 93) / ([C] / 12) is less than 0.2, the contribution of increasing the r-value due to the effect of refinement of hot-rolled sheet by Nb is reduced, and particularly in the range where the C content is high, The amount of dissolved C increases, which inhibits the formation of a recrystallized texture effective for increasing the r value, increases the hardness of the martensite phase, and makes it difficult to obtain a high λ value. Further, if ([Nb] / 93) / ([C] / 12) exceeds 0.7, the amount of C necessary to form a martensite phase is prevented from being present in the steel. A structure having the second phase including the site phase cannot be obtained.

  Therefore, the Nb content is set to 0.010 to 0.30%, and the Nb content and the C content are set to satisfy 0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7. It is supposed to be included. More preferably, Nb and C are contained so as to satisfy 0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.5.

3-100 × [C] ≦ Mn equivalent (%) ≦ 7-100 × [C], Mn equivalent (%) = [Mn]
However, [C] and [Mn] in the formula are the contents of each element (mass%)
The hardness of the second phase such as the martensite phase depends on the amount of solute C concentrated in the γ phase, and elements such as Mn, Cr, and Mo improve the hardenability of the steel sheet. The inventors have arranged the results of various experiments on the balance between the C content and the content of elements (Mn, etc.) that contribute to hardenability. In the steel sheet of the present invention, the elements that contribute to hardenability It was found that it is necessary to satisfy 3-100 × [C] ≦ Mn equivalent (%) ≦ 7-100 × [C]. That is, in the case of 3-100 × [C]> Mn equivalent (%), the second phase having hardness effective for the structure strengthening cannot be obtained. Further, when Mn equivalent (%)> 7-100 × [C], it becomes easy to obtain an excessively hard martensite phase that deteriorates stretch flangeability, and increases the addition cost of an alloy element that improves hardenability. In the basic composition of the present invention described above, Mn equivalent = [Mn].

The above is the basic composition of the high-strength steel sheet of the present invention.
In the present invention, one or more of Mo, Cr, Cu and Ni shown below may be added in addition to the above composition.

0.5% or less of one or more of Mo, Cr, Cu and Ni in total
Mo, Cr, Cu and Ni, like Mn, have the effect of slowing the critical cooling rate at which a martensite phase is obtained, and are elements that promote the formation of the martensite phase during cooling after annealing, and also improve the strength level. effective. In order to obtain such an effect, the total of Mo, Cr, Cu and Ni is preferably set to 0.05% or more. However, even if one or more elements are added in excess of 0.5% in total, these effects are not only saturated but also cost increases due to expensive components. The upper limit of the total content of two or more elements is preferably 0.5%. Here, Mo, Cr, Cu, and Ni are elements that improve the hardenability of the steel sheet in the same manner as Mn described above. When adding Mo, Cr, Cu, and Ni, as Mn equivalent, Mn equivalent = [Mn ] + 3.3 × [Mo] + 1.3 × [Cr] + 0.5 × [Cu] + 0.4 × [Ni], and 3-100 × [C] ≦ Mn as described above Equivalent (%) ≦ 7−100 × [C], Mn equivalent (%) = [Mn] +3.3 [Mo] + 1.3 × [Cr] + 0.5 × [Cu] + 0.4 × [Ni] It is necessary to.
In the present invention, in addition to the above composition, Ti may be added within a range that satisfies the following conditions.

Ti: 0.1% or less, and satisfies ([Ti] / 48) / {([S] / 32) + ([N] / 14)} ≦ 2.0, and [Ti ^* ] = [Ti ] −48 × {([N] / 14) + ([S] / 32)} Based on the effective Ti amount [Ti ^* ] represented by [Ti ^* ]> 0 instead of the above formula (1) 0.2 ≦ {([Nb] / 93) + ([Ti ^* ] / 48)} / ([C] / 12) ≦ 0.7 or [Ti ^* ] ≦ 0 and 0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (provided that [Ti], [S], [N], [Nb] and [C] in the formula are the contents of each element (mass %))
Ti is an element that has the effect of precipitating and fixing solute N as being equal to or greater than that of Al. To obtain this effect, Ti is preferably contained in an amount of 0.005% or more. In addition to forming TiC, Ti exhibits the effect of fixing S by forming TiS and / or Ti ₄ C ₂ S ₂ and contributing to improvement of workability. However, excessive addition of more than 0.1% of the expensive Ti component not only increases the cost, but also prevents the solid solution C necessary for the formation of the martensite phase from remaining in the steel due to the formation of TiC. The content is preferably 0.1% or less.

When the steel contains Ti: 0.1% or less, ([Ti] / 48) / {([S] / 32) + ([N] / 14)} ≦ 2.0 is satisfied and [ Based on the effective Ti amount [Ti ^* ] represented by Ti ^* ] = [Ti] −48 × {([N] / 14) + ([S] / 32)}, [Ti ^* ]> 0, 0.2 ≦ {([Nb] / 93) + ([Ti ^* ] / 48)} / ([C] / 12) ≦ 0.7, or [Ti ^* ] ≦ 0, 0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 is preferably satisfied. That is, in order not to prevent excessive Ti from leaving solid solution C in the steel, in relation to the contents of S and N that preferentially bond with Ti in the steel, ([Ti] / 48 ) / {([S] / 32) + ([N] / 14)} ≦ 2.0, [Ti ^* ]> 0 and 0.2 ≦ {([ Nb] / 93) + ([Ti ^* ] / 48)} / ([C] / 12) ≦ 0.7 or [Ti ^* ] ≦ 0 and 0.2 ≦ ([Nb] / 93) / ([C] / 12) It is preferable to add Ti so as to satisfy ≦ 0.7. When the value of ([Ti] / 48) / {([S] / 32) + ([N] / 14)} is larger than 2.0, excess Ti is combined with solute C, in the steel. This is because there is a possibility that the solid solution C cannot be left. The reason why [Ti ^* ]> 0 and 0.2 ≦ {([Nb] / 93) + ([Ti ^* ] / 48)} / ([C] / 12) ≦ 0.7 is limited to [Ti ^* ] > 0, and the value of {([Nb] / 93) + ([Ti ^* ] / 48)} / ([C] / 12) is less than 0.2, the solid solution C is particularly in a high C content range. This is because the abundance increases and the formation of {111} recrystallized texture effective for increasing the r value is inhibited, and {([Nb] / 93) + ([Ti ^* ] / 48)} / This is because if the value of ([C] / 12) is larger than 0.7, the presence of the amount of C in steel necessary for forming a martensite phase is prevented. Even if Ti is contained in the steel, if [Ti ^* ] ≦ 0, the effect of precipitation and fixation of C by Ti is small. In this case, the Ti content is taken into account. It is not necessary, and it is preferable that 0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 is satisfied as in the above formula (1).

  In the present invention, the balance other than the above-described components is preferably substantially composed of iron (Fe) and inevitable impurities.

  In addition, if it is in the normal steel composition range, even if it contains B, Ca, REM, etc., there is no problem. For example, B is an element having an effect of improving the hardenability of steel and can be contained as necessary. However, when the content exceeds 0.003%, the effect is saturated, and therefore it is preferably 0.003% or less.

  Moreover, Ca and REM have the effect | action which controls the form of a sulfide type inclusion, and, thereby, prevents the deterioration of the various characteristics of a steel plate. Since such an effect tends to be saturated when the content of one or two selected from Ca and REM exceeds 0.01% in total, it is preferable to make the content less than this.

  Other inevitable impurities include, for example, Sb, Sn, Zn, Co, etc. The allowable ranges of these contents are Sb: 0.01% or less, Sn: 0.1% or less, Zn: 0.01% or less , Co: 0.1% or less.

Next, the reason why the steel structure of the high-strength steel sheet of the present invention is limited will be described.
The high-strength steel sheet of the present invention is composed of a ferrite phase and a second phase as main phases, limited to the above steel composition, and the ratio of the hardness H (S) of the second phase to the hardness H (F) of the ferrite phase. H (S) / H (F) is in the range of 1.5 to 3.0, the area ratio of the ferrite phase to the entire structure is 50% or more, and the area ratio to the entire structure is 1 to 15 in the second phase. It is necessary to have a steel structure containing a% martensite phase.

  The high-strength steel sheet of the present invention has a good deep drawability and a steel sheet having a tensile strength of ≧ 440 MPa. Therefore, the high-strength steel sheet is composed of a ferrite phase as a main phase and a second phase. 50% or more, and a steel sheet having a steel structure containing a martensite phase of 1% or more, more preferably 3% or more, and 15% or less in terms of the area ratio relative to the entire structure in the second phase, so-called composite structure It must be a steel plate. In particular, in the present invention, an average r value ≧ 1.2 can be achieved by developing a {111} recrystallization texture of a ferrite phase occupying an area ratio of 50% or more. If the ferrite phase is less than 50% in area ratio, it becomes difficult to ensure good deep drawability. The ferrite phase is preferably 70% or more in terms of area ratio, and in order to utilize the advantages of the composite structure, the ferrite phase is preferably 97% or less in area ratio.

  On the other hand, in order to obtain a hole expansion ratio λ value ≧ 80%, the upper limit of the martensite phase is 15% or less in area ratio, desirably 12% or less, and the ratio of the ferrite phase to the second phase H (S) / H (F) needs to be in the range of 1.5 to 3.0. Here, the second phase means a phase other than the ferrite phase, which is the main phase, and includes a martensite phase. In addition, examples of phases other than the martensite phase in the second phase include a pearlite phase, a bainite phase, and a retained austenite phase.

  Here, the “ferrite phase” includes a polygonal ferrite phase and a bainitic ferrite phase having a high dislocation density transformed from an austenite phase.

  Moreover, in this invention, it is necessary for a martensite phase to exist and it is necessary to contain a martensite phase 1% or more by area ratio. When the martensite phase is less than 1%, it is difficult to obtain a good strength ductility balance. The martensite phase is preferably 3% or more. On the other hand, if the area ratio of the martensite phase exceeds 15%, the probability of void formation at the interface between the ferrite phase and the martensite phase increases even if the hardness ratio is adjusted, so that the hole expandability is deteriorated. For this reason, the martensite phase is 15% or less in terms of area ratio. In addition, in order to obtain a good hole expansion rate, the martensite phase obtained has a ratio H (S) / H (F) (average hardness) of the hardness H (F) of the ferrite phase and the hardness H (S) of the second phase. The ratio) is also required to be 1.5 to 3.0. If the average hardness ratio is less than 1.5, a good strength-ductility balance as a composite structure steel sheet cannot be obtained. If the average hardness ratio exceeds 3.0, locality at the interface between the phases having a large hardness ratio is not obtained. This is because the amount of plastic deformation increases, voids are generated, and the hole expandability deteriorates.

  In addition, as a method for controlling the average hardness ratio in the range of 1.5 to 3.0, for example, annealing of a relatively high temperature, softening of a hard phase by overaging in a temperature range of 200 to 400 ° C., NbC And strengthening of the matrix phase (soft phase) by precipitation strengthening.

  Here, the “average hardness ratio” is a ratio of values obtained by measuring the indentation hardness of the ferrite phase and the second phase using a hardness meter. Since the second phase obtained in the present invention is fine, a micro Vickers hardness meter that has been used for measuring the hardness of a minute region in the past is not impossible to measure, but has a large variation and a problem in accuracy. It is appropriate to use a nano hardness tester capable of measuring the hardness even when the size is 1 μm or less. A similar test was attempted with a micro Vickers hardness tester, but in the steel sheet of the present invention, there was no correlation between hardness and particularly hole expansibility.

  In addition, as described above, the second phase has a structure including a pearlite phase (P), a bainite phase (B), or a retained austenite phase (γ ′) in addition to the martensite phase (M) described above. Also good. In order to more fully demonstrate the effects of the ferrite phase and the martensite phase described above, it is preferable that the other phases are small, that is, it is preferable that the total area ratio of the ferrite phase and the martensite phase is high. The total rate is preferably 90% or more.

  The high-strength steel sheet of the present invention satisfying the above component composition and steel structure satisfies an average r value of 1.2 or more and a hole expansion ratio λ value of 80% or more.

Here, the “hole expansion ratio λ value” is obtained by performing a hole expansion test in accordance with the provisions of JFST 1001. That is, a punch hole punched out with a 10 mmφ punch is opened in the test piece, a conical punch with an apex angle of 60 ° is used, the burr is on the outside, and the hole is expanded until a crack that penetrates the plate thickness occurs. . At this time, d ₀ : initial hole inner diameter (mm), d: hole inner diameter (mm) at the time of occurrence of cracks, hole expansion ratio λ (%) = {(d−d ₀ ) / d ₀ } × 100 .

Here, the “average r value” means an average plastic strain ratio obtained by JIS Z 2254, and is a value calculated from the following formula.
Average r value = (r ₀ + 2r ₄₅ + r ₉₀ ) / 4
Here, r ₀ , r ₄₅ and r ₉₀ are plastic strain ratios obtained by measuring the test pieces in the 0 °, 45 ° and 90 ° directions with respect to the rolling direction of the plate surface, respectively.

  The high-strength steel sheet of the present invention includes a cold-rolled steel sheet, a steel sheet having a plating layer by performing a surface treatment such as electroplating or hot dip galvanizing, a so-called plated steel sheet, and the like. Here, “plating” means pure zinc, zinc-based alloy plating containing zinc as a main component and alloying elements, or pure Al, Al-based alloy plating containing Al as a main component and alloying elements, etc. In addition, a plating layer conventionally applied to the surface of a steel sheet is also included.

Next, the preferable manufacturing method of the high strength steel plate of this invention is demonstrated.
Since the composition of the steel slab used in the production method of the present invention is the same as that of the steel sheet described above, description of the reason for limiting the steel slab is omitted.

  The high-strength steel sheet of the present invention uses a steel slab having a composition within the above-described range as a raw material, hot-rolls the hot-rolled sheet by subjecting the raw material to hot rolling, and cold-rolls the hot-rolled sheet. It can manufacture by passing through the cold rolling process which makes a cold-rolled sheet, and the cold-rolled sheet annealing process which achieves recrystallization and composite organization to this cold-rolled sheet.

  In the present invention, the steel slab is first subjected to finish rolling at a finish rolling exit temperature of 800 ° C. or higher by hot rolling, and wound at a winding temperature of 400 to 720 ° C. to obtain a hot rolled sheet (hot Rolling process).

  The steel slab used in the production method of the present invention is preferably produced by a continuous casting method in order to prevent macro segregation of components, but may be produced by an ingot-making method or a thin slab casting method. Moreover, after manufacturing the steel slab, in addition to the conventional method of once cooling to room temperature and then heating again, the steel slab is charged directly into the heating furnace without being cooled and charged in a heating furnace. Energy-saving processes such as direct-rolling and direct rolling, in which hot rolling is performed immediately after heat retention, can also be applied without problems.

  The slab heating temperature is preferably low because the precipitates are coarsened to develop a {111} recrystallized texture and improve deep drawability. However, if the heating temperature is less than 1000 ° C., the rolling load increases and the risk of trouble during hot rolling increases, so the slab heating temperature is preferably 1000 ° C. or higher. Note that the upper limit of the slab heating temperature is preferably set to 1300 ° C. because of an increase in scale loss accompanying an increase in oxidized weight.

  Hot rough rolling is applied to the steel slab heated under the above conditions. Here, the steel slab is made into a sheet bar by hot rough rolling. The conditions for the hot rough rolling need not be specified, and may be performed according to a conventional method. From the viewpoint of lowering the slab heating temperature and preventing troubles during hot rolling, it is preferable to use a so-called sheet bar heater that heats the sheet bar.

  Next, the sheet bar is finish-rolled to obtain a hot-rolled sheet. At this time, it is preferable that finish rolling delivery temperature (FT) shall be 800 degreeC or more. This is to obtain a fine hot-rolled sheet structure that provides excellent deep drawability after cold rolling and annealing. If the FT is less than 800 ° C., the load during hot rolling becomes high, and the work recovery (ferrite) structure tends to remain in the hot rolled structure, which is the development of the {111} texture during cold rolling annealing. Hinder. Therefore, FT is preferably set to 800 ° C. or higher. In addition, when FT exceeds 980 ° C., the structure becomes coarse, and this also tends to hinder the formation and development of {111} recrystallized texture during cold rolling annealing. From the viewpoint of obtaining a high r value, The upper limit of FT is preferably 980 ° C.

  Moreover, in order to reduce the rolling load at the time of hot rolling, it is good also as lubrication rolling between some or all passes of finishing rolling. Performing the lubrication rolling is effective from the viewpoint of uniforming the shape of the steel sheet and homogenizing the material. The coefficient of friction during lubrication rolling is preferably in the range of 0.10 to 0.25. Furthermore, it is also preferable to use a continuous rolling process in which the adjacent sheet bars are joined and finish-rolled continuously. The application of the continuous rolling process is also desirable from the viewpoint of the operational stability of hot rolling.

  The coil winding temperature (CT) is in the range of 400 to 720 ° C. This is because the temperature range is appropriate for depositing NbC in the hot-rolled sheet. When CT exceeds 720 ° C., the crystal grains become coarse, resulting in a decrease in strength and hindering a high r value after cold rolling annealing. Further, when CT is less than 400 ° C., NbC is hardly precipitated, which is disadvantageous for increasing the r value. CT is preferably 550 to 680 ° C.

  As described above, by adjusting the component composition and hot rolling conditions, 1) 60% or more of the entire Nb content is precipitated in the hot-rolled sheet stage, and 2) the structure of the hot-rolled sheet has a small inclination angle. The average crystal grain size including the grain boundary can be 8 μm or less, which is advantageous for increasing the λ and increasing the r value.

1) The ratio of Nb content ([Nb] prc) ([% Nb prc]) to be deposited as NbC or the like in the total Nb content ([Nb] total) in the hot rolling stage is 60% or more. The amount of precipitated Nb ([Nb] prc) is obtained by chemical analysis (extraction analysis) of the hot-rolled sheet, and the ratio [% Nb prc] of the precipitated Nb amount is calculated by the following equation.

  Reducing the solute C in the stage before cold rolling and recrystallization is effective for increasing the r value, and in the present invention, precipitation fixation is attempted as NbC. It is considered that precipitation in the matrix also contributes to an increase in the r value, and in order to obtain such an effect, the amount of precipitated Nb is preferably 60% or more of the total Nb content. It should be noted that the upper limit of the amount of Nb deposited as NbC or the like is not a problem as long as the Nb content satisfies the upper limit ([Nb] / 93) / ([C] / 12) ≦ 0.7 of the appropriate range of Nb. Both the valuation and the formation of martensite phase after annealing contribute to the formation of the second phase including the martensite phase that does not impair the hole expansibility, especially C which is not precipitated and fixed as NbC is different from conventional DP steel Will do.

2) The hot rolled sheet has an average crystal grain size of 8 μm or less including a small tilt grain boundary. The crystal grain size generally has a tilt angle of 15 ° or more, a so-called large tilt grain boundary, a tilt angle of less than 15 °. Often referred to as a low-angle grain boundary. When the hot-rolled sheet structure of the present invention is observed by being corroded with a nital solution, the addition of Nb results in the presence of a wire (grain boundary) that is corroded deeply as usual and a wire that is shallowly corroded (grain boundary). As a result of EBSP (Electron Back Scatter Diffraction Pattern) analysis of the shallow corrosion line, it was found that the shallow corrosion line is a so-called small-angle grain boundary with an inclination of less than 15 °.
In conventional mild steel sheets, it is known that the r value increases as the crystal grain size of the hot-rolled sheet is refined. In the present invention, when the particle size is measured using all the grain boundaries observed by corrosion by the nital liquid as the grain boundaries, that is, when the grain size is measured including particularly the low-angle grain boundaries, the average crystal grain size is 8 μm. An effect appears in increasing the r value below. As the method of measuring the crystal grain size, nominal particle size d _n by the parallel plate thickness cross section in the rolling direction (L cross section) captures a microstructure with an optical microscope, pursuant to JIS G 0552 cleavage method Alternatively, it may be obtained using an apparatus such as EBSP (Electron Back Scatter Diffraction Pattern).

Next, the hot-rolled sheet is cold-rolled to form a cold-rolled sheet (cold rolling process).
In addition, before cold rolling, it is preferable to perform pickling in order to remove the scale of a hot-rolled sheet as usual.

  In addition, what is necessary is just to perform pickling on normal conditions. The cold rolling condition is not particularly limited as long as it can be a cold-rolled sheet having a desired dimension and shape, but the rolling reduction during cold rolling needs to be at least 40%, more preferably 50% or more. And A high cold rolling reduction ratio is generally effective for increasing the r value, and if the reduction ratio is less than 40%, the {111} recrystallization texture does not develop sufficiently, and it is difficult to obtain excellent deep drawability. Become. On the other hand, in this invention, the r value increases as the cold rolling reduction is increased up to 90%, but when it exceeds 90%, not only the effect is saturated, but also the load on the roll during cold rolling is increased. Therefore, the upper limit is preferably 90%.

  Next, the cold-rolled sheet is annealed at an annealing temperature of 800 to 950 ° C., and cooled at an average cooling rate of 5 ° C./s or higher from 800 ° C. to a temperature in the temperature range of 400 to 200 ° C. It cools after hold | maintaining at temperature for 1 second or more (cold rolled sheet annealing process).

  The annealing is preferably continuous annealing performed in a continuous annealing line in order to ensure the cooling rate required in the present invention, and needs to be performed in a temperature range of 800 to 950 ° C. In the present invention, by setting the annealing temperature, which is the highest temperature during annealing, to approximately 800 ° C. or higher, the (α−γ) two-phase region, that is, the structure containing a ferrite phase and a martensite phase after cooling. Can be higher than the temperature at which is obtained, and higher than the recrystallization temperature. That is, if it is less than 800 ° C., a sufficient martensite phase is not formed after cooling, or recrystallization is not completed and the texture of the ferrite phase cannot be adjusted, so that the r value cannot be increased. On the other hand, at a high temperature exceeding 950 ° C., the recrystallized grains are remarkably coarsened and the characteristics are remarkably deteriorated, or the developed recrystallized texture is randomized by transformation, and a high r value cannot be obtained.

  Moreover, it is preferable to hold | maintain for 1 to 300 seconds in the temperature range of 800-950 degreeC. By maintaining the holding time in the temperature range for 1 second or longer, recrystallization proceeds sufficiently and is sufficiently retained in the two-phase region of (α-γ), phase separation, and sufficient solution C to γ This is because it can promote the thickening. The holding time in the temperature range is more preferably 10 seconds or longer. On the other hand, when the holding time exceeds 300 seconds, the crystal grains become coarse and various properties such as strength and surface properties tend to deteriorate. For this reason, the upper limit of the holding time is preferably set to 300 seconds.

  From the viewpoint of forming a martensite phase, the cooling rate after annealing is cooled from 800 ° C. to a temperature in the temperature range of 400 to 200 ° C. with an average cooling rate of 5 ° C./s or higher. ) For at least 1 second. This is because if the average cooling rate is less than 5 ° C./s, a martensite phase is hardly formed, and a ferrite single-phase structure is formed, and the structure strengthening cannot be sufficiently obtained.

  In the present invention, since the presence of the second phase including the martensite phase is essential, the average cooling rate from 800 ° C. to the holding temperature needs to be equal to or higher than the critical cooling rate, and this is achieved. Is generally satisfied at 5 ° C./s or more. Here, the reason why the cooling start temperature is limited to 800 ° C. is that it is necessary to start cooling from the α-γ2 phase region in order to obtain a martensite phase. Below this temperature, it becomes difficult to obtain a second phase effective for strengthening the structure. In this sense, there is no problem even if cooling is performed at an cooling temperature of 5 ° C./s or higher from an annealing temperature of 800 ° C. or higher.

  In addition, after cooling to a holding temperature of 400 to 200 ° C. at a cooling rate of an average cooling rate of 5 ° C./s or more, even when holding at that temperature for 1 second or more, if the holding temperature is 300 ° C. or more, The average cooling rate is preferably 5 ° C./s or higher up to 300 ° C. The reason why the holding temperature is in the temperature range of 400 to 200 ° C. is that if it exceeds 400 ° C., it is difficult to obtain a hard martensite phase effective as a structure strengthening. This is because no phase is obtained, or the average hardness ratio H (S) / H (F) of the hardness H (S) of the second phase to the hardness H (F) of the ferrite phase is larger than 3.0. Furthermore, the holding time at the holding temperature is 1 second or longer in order to promote the formation of a so-called low-temperature transformation phase such as a martensite phase having a low internal stress or a low-temperature bainite phase. The holding time is more preferably 10 seconds or longer. The upper limit of the holding time is not particularly limited, but it is preferably 600 seconds or less because of saturation of the above effects, softening of the generated martensite phase and production cost.

  Moreover, after the said cold rolling annealing process, surface treatments, such as an electroplating process or a hot dipping process, may be given and a plating layer may be formed in the steel plate surface.

  Here, the plating layer is not limited to pure zinc plating or zinc-based alloy plating, but can of course be various plating layers conventionally applied to the steel sheet surface such as Al or Al-based alloy plating.

  Further, the cold-rolled steel sheet (also referred to as cold-rolled annealed sheet) or the plated steel sheet manufactured as described above may be subjected to temper rolling or leveler processing for the purpose of adjusting the shape correction, surface roughness, and the like. The total elongation of temper rolling or leveler processing is preferably in the range of 0.2 to 15%. If it is less than 0.2%, the intended purpose of shape correction and roughness adjustment may not be achieved. On the other hand, if it exceeds 15%, it tends to cause a significant decrease in ductility. In addition, although the processing form differs between temper rolling and leveler processing, it has been confirmed that there is no significant difference in the effect between the two. Temper rolling and leveler processing may be performed after the plating treatment.

  The above description is merely an example of the embodiment of the present invention, and various modifications can be made within the scope of the claims.

Next, examples of the present invention will be described.
Molten steel having the composition shown in Table 1 was melted in a converter and made into a slab by a continuous casting method. These steel slabs were heated to 1250 ° C. and roughly rolled into sheet bars, and then hot-rolled sheets were formed by a hot rolling process in which finish rolling under the conditions shown in Tables 2 and 3 was performed. These hot-rolled sheets were pickled and cold-rolled at a rolling reduction of 65% to obtain cold-rolled sheets by a rolling process. Subsequently, these cold rolled sheets were subjected to continuous annealing in the continuous annealing line under the conditions shown in Tables 2 and 3. Next, the obtained cold-rolled annealed sheet was subjected to temper rolling with an elongation of 0.5%, and various properties were evaluated. The steel plates No. 2 and 12 were annealed, pickled, and 750 ° C. in an atmosphere containing dew point: −40 ° C., 7 vol% H ₂ and the balance being N ₂ in a hot dip galvanizing facility. After the plating pretreatment for 40 seconds, the hot dip galvanization was performed by immersing in a hot dip galvanizing bath having a bath temperature of 470 ° C. and an Al content of 0.14 mass% for a plating time of 1 second.

  Tables 2 and 3 show the results of investigations on the microstructure, hardness measurement, tensile properties, hole expansion ratio λ value, and r value of each cold-rolled annealed plate and hot-dip galvanized steel plate. Moreover, about the hot-rolled sheet after a hot rolling process, the ratio of the amount of C precipitated and fixed as NbC and the microstructure (crystal grain size) were examined by the method described above. The crystal grain size was measured by a cutting method according to JIS G 0552.

抽出分析の方法は、マレイン酸系電解液を用いて電解抽出した残渣をアルカリ融解し、融成物を酸溶解した後、ICP発光分光法で定量した。 The survey method is as follows.
(I) Calculation of the ratio of precipitated Nb amount [% Nb prc] Precipitated Nb amount ([Nb] prc) obtained by chemical analysis (extraction analysis) of hot-rolled sheet, Nb amount in steel ([Nb] total) Then, the ratio [% Nb prc] of the precipitated Nb amount is calculated by the following formula.

The extraction analysis was performed by ICP emission spectrometry after the residue obtained by electrolytic extraction with a maleic acid electrolyte was alkali-melted and the melt was acid-dissolved.

(Ii) Measurement of average crystal grain size of hot-rolled sheet With respect to a sheet thickness section (L section) parallel to the rolling direction, the microstructure was imaged using an optical microscope or a scanning electron microscope, and conforming to JIS G 0552 The average section length l (μm) of the crystal grains was determined by a cutting method, and the nominal particle diameter d _n = 1.13 × l was determined.

(Iii) Microstructure of cold-rolled annealed plates Test specimens were taken from each cold-rolled annealed plate, and the plate thickness cross section (L cross section) parallel to the rolling direction was measured using an optical microscope or a scanning electron microscope. The microscopic tissue was imaged at a magnification, the type of phase was observed, and the fraction of the second phase was determined from a 1000-3000 magnification image using a point counting method (point calculation method).

(Iv) Hardness measurement Specimens were taken from each of the obtained cold-rolled annealed plates, ground from the surface to a thickness of 1/4 position, and after grinding strain was removed by electrolytic polishing, using TRIBOSCOPE from Hysitron, The hardness of the ferrite phase and the second phase was measured, and the average hardness ratio was determined from the average value of each. The measurement was performed with the indentation size almost constant. Specifically, the hardness was measured by adjusting the load so that the indentation depth (= contact depth) proportional to the size of the indentation was 50 ± 10 nm. At this time, one side of the indentation is about 350 nm. In addition, when the structure was clearly unsuitable, for example, no martensite phase was observed by observation of the microscopic structure, no measurement was performed.

(V) Tensile properties JIS No. 5 tensile test specimens were sampled from each of the obtained cold-rolled annealed plates in the 90 ° direction (C direction) with respect to the rolling direction, and the crosshead speed was 10 mm / in accordance with the provisions of JIS Z 2241. A tensile test was performed at min, and yield stress (YS), tensile strength (TS), and elongation (El) were determined.

(Vi) λ value A 100 mm square test piece was taken from each of the obtained cold-rolled annealed plates and subjected to a hole expansion test in accordance with the provisions of the Japan Iron and Steel Federation Standard JFST 1001. In other words, a punch hole punched out with a 10mmφ punch is opened on the specimen, and a conical punch with an apex angle of 60 ° is used so that the burr is on the outside, and the hole is expanded until a crack that penetrates the plate thickness occurs. D ₀ : initial hole inner diameter (mm), d: hole inner diameter (mm) when cracking occurred, hole expansion ratio λ (%) = {(d−d ₀ ) / d ₀ } × 100 .

(Vii) r value JIS No. 5 tensile specimen from rolling direction (L direction), 45 ° direction (D direction) with respect to rolling direction, and 90 ° direction (C direction) with respect to rolling direction. Were collected. Measure the width strain and plate thickness strain of each specimen when 10% uniaxial tensile strain was applied to these specimens, and use these measurements to determine the average r value in accordance with JIS Z 2254 regulations. (Average plastic strain ratio) was calculated and used as the r value.

  As is clear from the investigation results shown in Tables 2 and 3, in the examples of the present invention, the TS is 440 MPa or more, the λ value is 80% or more, and the average r value is 1.2 or more. Excellent in both sex. On the other hand, in the comparative example manufactured under conditions outside the scope of the present invention, the strength is insufficient, the λ value is less than 80, or the r value is less than 1.2, and at least the stretch flangeability and the deep drawability. One is inferior.

  According to the present invention, even when the tensile strength TS is 440 MPa or more, or even higher strength TS500 MPa or more and TS590 MPa or more, the λ value is 80% or more, the average r value is 1.2 or more, stretch flangeability and deep drawing It is possible to produce a high-strength steel sheet excellent in both properties and excellent in overall formability at a low cost and with a remarkable industrial effect. For example, when the high-strength steel sheet of the present invention is applied to automobile parts, it is possible to increase the strength of complex parts that have been difficult to press-form so far, and can sufficiently contribute to collision safety and weight reduction of an automobile body. effective. Moreover, it is applicable not only to automobile parts but also to household appliance parts and pipe materials.

It is a figure which shows the relationship between ([Nb] / 93) / ([C] / 12) and average hardness ratio, (lambda) value, and average r value in the steel plate containing various C content.

Claims (8)

% By mass
C: 0.010 to 0.050%
Si: 1.0% or less,
Mn: 1.0-3.0%
P: 0.005-0.1%
S: 0.01% or less,
Al: 0.005-0.5%
N: 0.01% or less and
Nb: 0.01-0.3%
And the following formulas (1), (2) and (3) are satisfied, the balance has a component composition consisting of Fe and inevitable impurities, and consists of a ferrite phase and a second phase as main phases, The ratio H (S) / H (F) of the hardness H (S) of the second phase to the hardness H (F) of the ferrite phase is in the range of 1.5 to 3.0, and the area ratio of the ferrite phase to the entire structure is 50%. A high-strength steel sheet excellent in deep drawability and stretch flangeability, characterized in that the second phase has a steel structure containing a martensite phase in an area ratio of 1 to 15% with respect to the entire structure.
Record
0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (1)
3-100 × [C] ≦ Mn equivalent (%) ≦ 7-100 × [C] (2)
Mn equivalent (%) = [Mn] (3)
However, [Nb], [C] and [Mn] in the formula are the contents (mass%) of each element. % By mass
C: 0.010 to 0.050%
Si: 1.0% or less,
Mn: 1.0-3.0%
P: 0.005-0.1%
S: 0.01% or less,
Al: 0.005-0.5%
N: 0.01% or less and
Nb: 0.01-0.3%
In addition, one or more of Mo, Cr, Cu and Ni is contained in a total of 0.5% or less, and the following formulas (1), (2) and (4) are satisfied, and the balance is It has a composition composed of Fe and inevitable impurities, and consists of a ferrite phase and a second phase, which are the main phases, and the ratio of the hardness H (S) of the second phase to the hardness H (F) of the ferrite phase H (S) / H (F) is in the range of 1.5 to 3.0, the area ratio of the ferrite phase to the entire structure is 50% or more, and the martensite is 1 to 15% in the area ratio of the entire structure in the second phase. A high-strength steel sheet excellent in deep drawability and stretch flangeability, characterized by having a steel structure containing a phase.
Record
0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (1)
3-100 × [C] ≦ Mn equivalent (%) ≦ 7-100 × [C] (2)
Mn equivalent (%) = [Mn] + 3.3 x [Mo] + 1.3 x [Cr] + 0.5 x [Cu] + 0.4 x [Ni] (4)
However, [Nb], [C], [Mn], [Mo], [Cr], [Cu] and [Ni] in the formula are the contents (mass%) of each element. In addition to the above composition, further containing Ti: 0.1% by mass or less, satisfying the following formula (5), and based on the effective Ti amount [Ti ^* ] represented by the following formula (6), The high-strength steel sheet excellent in deep drawability and stretch flangeability according to claim 1 or 2, wherein the following formula (7) or the following formula (8) is satisfied instead of the formula (1).
([Ti] / 48) / {([S] / 32) + ([N] / 14)} ≦ 2.0 (5)
[Ti ^* ] = [Ti] −48 × {([N] / 14) + ([S] / 32)} (6)
[Ti ^* ]> 0, 0.2 ≦ {([Nb] / 93) + ([Ti ^* ] / 48)} / ([C] / 12) ≦ 0.7 (7)
[Ti ^* ] ≤0, 0.2≤ ([Nb] / 93) / ([C] / 12) ≤0.7 (8)
However, [Ti], [S], [N], [Nb], and [C] in the formula are the contents (mass%) of each element.   The high-strength steel sheet excellent in deep drawability and stretch flangeability according to any one of claims 1 to 3, wherein the surface has a plating layer. % By mass
C: 0.010 to 0.050%
Si: 1.0% or less,
Mn: 1.0-3.0%
P: 0.005-0.1%
S: 0.01% or less,
Al: 0.005-0.5%
N: 0.01% or less and
Nb: 0.01-0.3%
Contain, and the following (1), (2) and (3) meets the equation, balance finishing a steel slab having a composition consisting of Fe and unavoidable impurities by hot rolling rolling delivery temperature: 800 A finish rolling is performed at a temperature of ℃ or higher, a coiling temperature is wound at 400 to 720 ℃, a hot rolling step to be a hot rolled sheet, and the hot rolled sheet is subjected to a cold rolling at a rolling reduction of 40% or more, Cold rolling process for forming a cold-rolled sheet, and annealing the cold-rolled sheet at an annealing temperature of 800 to 950 ° C, and then from 800 ° C to a temperature in the temperature range of 400 to 200 ° C, an average cooling rate: 5 ° C A method for producing a high-strength steel sheet excellent in deep drawability and stretch flangeability, characterized by sequentially performing a cold-rolled sheet annealing step of cooling at / s or higher, and then cooling after holding at the temperature for 1 second or longer.
Record
0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (1)
3-100 × [C] ≦ Mn equivalent (%) ≦ 7-100 × [C] (2)
Mn equivalent (%) = [Mn] (3)
However, [Nb], [C] and [Mn] in the formula are the contents (mass%) of each element. % By mass
C: 0.010 to 0.050%
Si: 1.0% or less,
Mn: 1.0-3.0%
P: 0.005-0.1%
S: 0.01% or less,
Al: 0.005-0.5%
N: 0.01% or less and
Nb: 0.01-0.3%
Contains further Mo, Cr, containing 0.5% in total of one or more of Cu and Ni, and the following (1), meets the (2) and (4), the balance Is a steel slab having a composition composed of Fe and inevitable impurities , hot-rolled to finish rolling to a finish rolling exit temperature of 800 ° C or higher, wound at a winding temperature of 400 to 720 ° C, hot rolled A cold rolling step in which the hot-rolled sheet is cold-rolled at a rolling reduction of 40% or more to obtain a cold-rolled sheet, and the cold-rolled sheet is annealed at a temperature of 800 to 950 ° C. A cold-rolled sheet annealing step in which annealing is performed, and then cooling is performed at an average cooling rate of 5 ° C./s or higher from 800 ° C. to a temperature in the range of 400 to 200 ° C. A method for producing a high-strength steel sheet excellent in deep drawability and stretch flangeability, characterized by sequentially applying.
Record
0.2 ≦ ([Nb] / 93) / ([C] / 12) ≦ 0.7 (1)
3-100 × [C] ≦ Mn equivalent (%) ≦ 7-100 × [C] (2)
Mn equivalent (%) = [Mn] + 3.3 x [Mo] + 1.3 x [Cr] + 0.5 x [Cu] + 0.4 x [Ni] (4)
However, [Nb], [C], [Mn], [Mo], [Cr], [Cu] and [Ni] in the formula are the contents (mass%) of each element. In addition to the above composition, further containing Ti: 0.1% by mass or less, satisfying the following formula (5), and based on the effective Ti amount [Ti ^* ] represented by the following formula (6), The method for producing a high-strength steel sheet excellent in deep drawability and stretch flangeability according to claim 5 or 6, wherein the following formula (7) or the following formula (8) is satisfied instead of formula (1): .
([Ti] / 48) / {([S] / 32) + ([N] / 14)} ≦ 2.0 (5)
[Ti ^* ] = [Ti] −48 × {([N] / 14) + ([S] / 32)} (6)
[Ti ^* ]> 0, 0.2 ≦ {([Nb] / 93) + ([Ti ^* ] / 48)} / ([C] / 12) ≦ 0.7 (7)
[Ti ^* ] ≤0, 0.2≤ ([Nb] / 93) / ([C] / 12) ≤0.7 (8)
However, [Ti], [S], [N], [Nb], and [C] in the formula are the contents (mass%) of each element.   The deep drawing property and stretch flangeability according to any one of claims 5 to 7, further comprising a plating treatment step of forming a plating layer on the surface of the steel sheet after the cold rolled sheet annealing step. A method for producing high strength steel sheets.

Images