Patent Application
20120107633
This disclosure relates to high-strength steel sheets having excellent stretch flangeability after working and a tensile strength (TS) of 980 MPa or more and methods for manufacturing such high-strength steel sheets.
Conventionally, 590 MPa grade steels have been used for automotive chassis and impact members such as bumpers and center pillars because they demand formability (mainly ductility and stretch flangeability). Recently, however, the use of automotive steel sheets with higher strengths has been promoted to reduce the effects of automobiles on the environment and to improve crashworthiness, and research on the use of 980 MPa grade steels has been started. In general, a steel sheet having a higher strength has a lower workability. Therefore, steel sheets having high strength and high workability have been currently researched. Examples of techniques for improving ductility and stretch flangeability include the following techniques.
Japanese Unexamined Patent Application Publication No. 2007-063668 discloses a technique related to a high-tensile-strength steel sheet having a tensile strength of 980 MPa or more, the steel sheet being composed substantially of a ferritic single-phase structure and having carbides of an average grain size of less than 10 nm precipitated and dispersed therein, the carbides containing titanium, molybdenum, and vanadium and having an average composition satisfying V/(Ti+Mo+V)≧0.3, where Ti, Mo, and V are expressed in atomic percent.
Japanese Unexamined Patent Application Publication No. 2006-161112 discloses a technique related to a high-strength hot-rolled steel sheet having a strength of 880 MPa or more and a yield ratio of 0.80 or more, the steel sheet having a steel composition containing, by mass, 0.08% to 0.20% of carbon, 0.001% to less than 0.2% of silicon, more than 1.0% to 3.0% of manganese, 0.001% to 0.5% of aluminum, more than 0.1% to 0.5% of vanadium, 0.05% to less than 0.2% of titanium, and 0.005% to 0.5% of niobium and satisfying inequalities (a), (b), and (c), the balance being iron and impurities, and a steel structure containing 70% by volume or more of ferrite having an average grain size of 5 μm or less and a hardness of 250 Hv or more:
9(Ti/48+Nb/93)×C/12≦4.5×10−5 Inequality (a):
0.5%≦(V/51+Ti/48+Nb/93)/(C/12)≦1.5 Inequality (b):
V+Ti×2+Nb×1.4+C×2+Mn×0.1≧0.80. Inequality (c):
Japanese Unexamined Patent Application Publication No. 2004-143518 discloses a technique related to a hot-rolled steel sheet containing, in mass percent, 0.05% to 0.2% of carbon, 0.001% to 3.0% of silicon, 0.5% to 3.0% of manganese, 0.001% to 0.2% of phosphorus, 0.001% to 3% of aluminum, more than 0.1% to 1.5% of vanadium, and optionally 0.05% to 1.0% of molybdenum, the balance being iron and impurities, the steel sheet having a structure containing ferrite having an average grain size of 1 to 5 μm as a primary phase, the ferrite grains containing vanadium carbonitrides having an average grain size of 50 nm or less.
Japanese Unexamined Patent Application Publication No. 2004-360046 discloses a technique related to a high-strength steel sheet having a tensile strength of 880 MPa or more in a direction perpendicular to a rolling direction and a yield ratio of 0.8 or more, the steel sheet having a steel composition containing, in mass percent, 0.04% to 0.17% of carbon, 1.1% or less of silicon, 1.6% to 2.6% of manganese, 0.05% or less of phosphorus, 0.02% or less of sulfur, 0.001% to 0.05% of aluminum, 0.02% or less of nitrogen, 0.11% to 0.3% of vanadium, and 0.07% to 0.25% of titanium, the balance being iron and incidental impurities.
Japanese Unexamined Patent Application Publication No. 2005-002406 discloses a technique related to a high-strength hot-rolled steel sheet having a strength of 880 MPa or more and a yield ratio of 0.80 or more, the steel sheet having a steel composition containing, in mass percent, 0.04% to 0.20% of carbon, 0.001% to 1.1% of silicon, more than 0.8% of manganese, 0.05% to less than 0.15% of titanium, and 0% to 0.05% of niobium and satisfying inequalities (d), (e), and (f), the balance being iron and incidental impurities:
(Ti/48+Nb/93)×C/12≦3.5×10−5 Inequality (d):
0.4≦(V/51+Ti/48+Nb/93)/(C/12)≦2.0 Inequality (e):
V+Ti×2+Nb×1.4+C×2+Si×0.2+Mn×0.1≧0.7. Inequality (f):
Japanese Unexamined Patent Application Publication No. 2005-232567 discloses a technique related to an ultrahigh-tensile-strength steel sheet with excellent stretch flangeability having a tensile strength of 950 MPa or more, the steel sheet being composed substantially of a ferritic single-phase structure, the ferritic structure having precipitates containing titanium, molybdenum, and carbon precipitated therein, wherein the area fraction of <110> colonies of adjacent crystal grains in a region between a position one-fourth of the thickness and a position three-fourths of the thickness in a cross section perpendicular to a vector parallel to a rolling direction is 50% or less.
Japanese Unexamined Patent Application Publication No. 2006-183138 discloses a technique related to a steel sheet having a composition containing, in mass percent, 0.10% to 0.25% of carbon, 1.5% or less of silicon, 1.0% to 3.0% of manganese, 0.10% or less of phosphorus, 0.005% or less of sulfur, 0.01% to 0.5% of aluminum, 0.010% or less of nitrogen, and 0.10% to 1.0% of vanadium and satisfying (10Mn+V)/C≧50, the balance being iron and incidental impurities, wherein the average grain size of carbides containing vanadium determined for precipitates having a grain size of 80 nm or less is 30 nm or less.
Japanese Unexamined Patent Application Publication No. 2006-183139 discloses a technique related to an automotive member having a composition containing, in mass percent, 0.10% to 0.25% of carbon, 1.5% or less of silicon, 1.0% to 3.0% of manganese, 0.10% or less of phosphorus, 0.005% or less of sulfur, 0.01% to 0.5% of aluminum, 0.010% or less of nitrogen, and 0.10% to 1.0% of vanadium and satisfying (10 Mn+V)/C≧50, the balance being iron and incidental impurities, wherein the volume fraction of tempered martensite phase is 80% or more, and the average grain size of carbides containing vanadium and having a grain size of 20 nm or less is 10 nm or less.
Japanese Unexamined Patent Application Publication No. 2007-016319 discloses a technique related to high-tensile-strength hot-dip galvanized steel sheet having a hot-dip galvanized layer thereon, the steel sheet having a chemical composition containing, in mass percent, more than 0.02% to 0.2% of carbon, 0.01% to 2.0% of silicon, 0.1% to 3.0% of manganese, 0.003% to 0.10% of phosphorus, 0.020% or less of sulfur, 0.001% to 1.0% of aluminum, 0.0004% to 0.015% of nitrogen, and 0.03% to 0.2% of titanium, the balance being iron and impurities, the steel sheet having a metallographic structure containing 30% to 95% by area of ferrite, wherein if second phases in the balance include martensite, bainite, pearlite, and cementite, the area fraction of martensite is 0% to 50%, the steel sheet containing titanium-based carbonitride precipitates having a grain size of 2 to 30 nm with an average intergrain distance of 30 to 300 nm and crystallized TiN having a grain size of 3 μm or more with an average intergrain distance of 50 to 500 μm.
Japanese Unexamined Patent Application Publication No. 2003-105444 discloses a technique related to a method for improving the fatigue resistance of a steel sheet, including subjecting a steel sheet to strain aging treatment to form fine precipitates having a grain size of 10 nm or less, the steel sheet having a composition containing, in mass percent, 0.01% to 0.15% of carbon, 2.0% or less of silicon, 0.5% to 3.0% of manganese, 0.1% or less of phosphorus, 0.02% or less of sulfur, 0.1% or less of aluminum, 0.02% or less of nitrogen, and 0.5% to 3.0% of copper and having a multiphase structure containing ferrite phase as a primary phase and a phase containing 2% by area or more of martensite phase as a second phase.
Japanese Unexamined Patent Application Publication No. 4-289120 discloses a technique related to a method for manufacturing an ultrahigh-strength cold-rolled steel sheet with good formability and strip shape having a fine two-phase structure containing 80% to 97% by volume of martensite, the balance being ferrite, and a tensile strength of 150 to 200 kgf/mm2, the method including hot-rolling a steel at a finishing temperature higher than or equal to the Ar3 point, coiling the steel at 500° C. to 650° C., pickling the steel, cold-rolling the steel, performing continuous annealing by heating the steel to Ac3 to [Ac3+70° C.] and soaking the steel for 30 seconds or more, performing first cooling to precipitate 3% to 20% by volume of ferrite, quenching the steel to room temperature in a jet of water, and subjecting the steel to overaging treatment at 120° C. to 300° C. for 1 to 15 minutes, the steel containing, in mass percent, 0.18% to 0.3% of carbon, 1.2% or less of silicon, 1% to 2.5% of manganese, 0.02% or less of phosphorus, 0.003% or less of sulfur, and 0.01% to 0.1% of dissolved aluminum and further containing one or more of 0.005% to 0.030% of niobium, 0.01% to 0.10% of vanadium, and 0.01% to 0.10% of titanium in a total amount of 0.005% to 0.10%, the balance being iron and incidental impurities.
Japanese Unexamined Patent Application Publication No. 2003-096543 discloses a technique related to a high-strength hot-rolled steel sheet having high bake hardenability at high prestrain, the steel sheet containing, in mass percent, 0.0005% to 0.3% of carbon, 0.001% to 3.0% of silicon, 0.01% to 3.0% of manganese, 0.0001% to 0.3% of aluminum, 0.0001% to 0.1% of sulfur, and 0.0010% to 0.05% of nitrogen, the balance being iron and incidental impurities, wherein ferrite has the largest area fraction, dissolved carbon, Sol. C, and dissolved nitrogen, Sol. N, satisfy Sol.C/Sol.N=0.1 to 100, and the average or each of the amounts of increase in yield strength and tensile strength after prestraining to 5% to 20% and baking at 110° C. to 200° C. for 1 to 60 minutes is 50 MPa or more as compared to the steel sheet before prestraining and baking
However, the known techniques described above have the following problems.
The steels described in JP '668, JP '112 and JP '518, which contain molybdenum, noticeably increase cost because the price of molybdenum has been rising recently. In addition, steel sheets for automotive applications have been used in severely corrosive environments in foreign countries as the automotive industry has globalized, which demands higher corrosion resistance after coating of steel sheets. The addition of molybdenum, however, cannot meet the above demand because it impairs formation or growth of conversion crystals, thus decreasing the corrosion resistance after coating of the steel sheets. Therefore, the steels described in JP '668, JP '112 and JP '518 do not satisfactorily meet the recent demand in the automotive industry.
On the other hand, a working process including, in sequence, drawing or stretch forming, piercing, and flange forming has been employed with the recent advances in pressing technology. This working process requires the portion of a steel sheet subjected to stretch flanging to have stretch flangeability after drawing or stretch forming and piercing, that is, after working The steels described in JP '668, JP '112, JP '518, JP '046, JP '406, JP '567, JP '138, JP '139, JP '319, JP '444, JP '120 and JP '543, however, do not necessarily have sufficient stretch flangeability after working because this property has only recently been noted.
Among the common techniques for strengthening steel is precipitation strengthening. It is known that the amount of precipitation strengthening is inversely proportional to the grain size of precipitates and is proportional to the square root of the amount of precipitate. For example, the steels disclosed in JP '668, JP '112, JP '518, JP '046, JP '406, JP '567, JP '138, JP '139, JP '319, JP '444, JP '120 and JP '543 contain carbonitride-forming elements such as titanium, vanadium, and niobium; particularly, JP '138, JP '319 and JP '444 have conducted research on the size of precipitates. However, the amount of precipitate is not necessarily sufficient. A high cost due to low precipitation efficiency is problematic.
Niobium, added in JP '112, JP '406 and JP '120, significantly inhibits recrystallization of austenite after hot rolling. This causes a problem in that it leaves unrecrystallized grains in the steel, thus decreasing workability, and also causes a problem in that the rolling load in hot rolling is increased.
In light of the above circumstances, it could be helpful to provide a high-strength steel sheet having excellent stretch flangeability after working and a method for manufacturing such a steel sheet.
As a result of our study in providing a high-strength steel sheet having excellent stretch flangeability after working and a tensile strength of 980 MPa or more, we discovered the following findings:
We thus provide:
T1≦0.06×T2+764 inequality (1)
The percentages used herein for steel compositions are all expressed by mass. In addition, the term “high-strength steel sheet” as used herein refers to a steel sheet having a tensile strength (hereinafter also referred to as “TS”) of 980 MPa or more and includes hot-rolled steel sheets and those subjected to surface treatment such as plating, that is, surface-treated steel sheets.
In addition, we achieve stretch flangeability (λ10) of 40% or more after rolling to an elongation of 10%.
Accordingly, a high-strength steel sheet having excellent stretch flangeability after working and a TS of 980 MPa or more can be provided. Our steel sheets and methods allow for cost reduction because the above advantages are achieved without adding molybdenum. When used for applications such as automotive chassis, frames for trucks, and impact members, our high-strength steel sheet allows a reduction in thickness, thus reducing the effects of automobiles on the environment, and significantly improves crashworthiness.
In addition to the compositional limitations described later, a high-strength steel sheet is characterized in that the metallographic structure thereof includes 80% to 98% by volume of a ferrite phase and a second phase, in that the sum of the amounts of titanium and vanadium contained in precipitates having a size of less than 20 nm is 0.150% by mass or more, and in that the difference (HVα−HVS) between the hardness (HVα) of the ferrite phase and the hardness (HVS) of the second phase is −300 to 300.
Thus, in addition to the compositional limitations and the structural fractions, we provide that the amounts of titanium and vanadium contained in precipitates having a size of less than 20 nm and the hardness difference (HVα−HVS). With these specified properties, which are the most important requirements, a high-strength steel sheet is provided that has excellent stretch flangeability after working and a TS of 980 MPa or more.
Next, our steel sheets and methods will be described in more detail based on experimental results.
We found that the hardness difference (HVα−HVS) is important for improved stretch flangeability after working Therefore, the hardness difference (HVα−HVS) and the stretch flangeability after working were examined.
Steels of compositions containing 0.09% to 0.185% by mass of carbon, 0.70% to 0.88% by mass of silicon, 1.00% to 1.56% by mass of manganese, 0.01% by mass of phosphorus, 0.0015% by mass of sulfur, 0.03% by mass of aluminum, 0.090% to 0.178% by mass of titanium, and 0.225% to 0.770% by mass of vanadium, with the balance being iron and incidental impurities, were prepared in a converter and were continuously cast into steel slabs. The steel slabs were then heated at a slab heating temperature of 1,250° C. and were hot-rolled at a finishing temperature of 890° C. to 950° C. The steel sheets were then subjected to first cooling to 635° C. to 810° C. at a cooling rate of 55° C./s, were cooled with air for two to six seconds, were subjected to second cooling at a cooling rate of 40° C./s, and were coiled at 250° C. to 600° C. to form hot-rolled steel sheets having a thickness of 2.0 mm. The resulting hot-rolled steel sheets were examined for the difference (HVα−HVS) between the hardness (HVα) of the ferrite phase and the hardness (HVS) of a second phase and stretch flangeability after working.
Vickers hardness was used as the difference (HVα−HVS) between the hardness of the ferrite phase (HVα) and the hardness of a second phase (HVS). The tester used for the Vickers hardness test was one complying with JIS B7725. A sample for structural examination was taken, the structure thereof was developed with a 3% natal solution in a cross section parallel to the rolling direction, and dents were made on ferrite grains and second phases at a position one-fourth of the thickness at a test load of 3 g. The hardness was calculated from the diagonal length of the dents using the Vickers hardness calculation formula in JIS Z2244. The hardnesses of 30 ferrite grains and 30 second phases were measured, and the averages thereof were used as the hardness (HVα) of the ferrite phase and the hardness (HVS) of the second phase to determine the hardness difference (HVα−HVS).
As the stretch flangeability after working, λ10 was determined by taking three specimens for a hole expanding test, rolling the specimens to an elongation of 10%, carrying out a hole expanding test according to Japan Iron and Steel Federation Standard JFS T1001, and calculating the average of the three pieces.
The results thus obtained are shown in
However, some hot-rolled steel sheets having a hardness difference (HVα−HVS) of −300 to 300 do not have a stretch flangeability after working of about 40% or more. In
Of the hot-rolled steel sheets produced in the above experiment, those having a hardness difference (HVα−HVS) of −300 to 300 were examined for the volume fraction of ferrite as a structural fraction. The volume fraction of ferrite was determined by developing the cross sectional microstructure parallel to the rolling direction with 3% natal, examining the microstructure at a position one-fourth of the thickness using a scanning electron microscope (SEM) at a magnification of 1,500×, and measuring the area fraction of ferrite as the volume fraction using the image processing software “Particle Analysis II” manufactured by Sumitomo Metal Technology Inc.
The obtained results are shown in
The above results demonstrated that it is important to specify the volume fraction of ferrite as well as the difference (HVα−HVS) between the hardness of the ferrite phase (HVα) and the hardness of the second phase (HVS) to achieve excellent stretch flangeability after working and that stretch flangeability after working of 40% or more is ensured if the difference (HVα−HVS) between the hardness of the ferrite phase (HVα) and the hardness of the second phase is −300 to 300 and the volume fraction of ferrite is 80% to 98%.
The reason why stretch flangeability after working improves if the hardness difference (HVα−HVS) and the volume fraction of ferrite are specified as described above is assumed as follows. If the volume fraction of ferrite exceeds 98%, although the reason is unclear, the stretch flangeability after working does not improve probably because numerous voids are formed at interfaces between ferrite phases. On the other hand, if the volume fraction of ferrite falls below 80%, stretch flangeability after working does not improve probably because extended second phases tend to form, joining together voids formed at interfaces between the ferrite phases and the second phases during working.
In addition to stretch flangeability after working, we achieve a high strength, namely, TS≧980. Therefore, means for achieving high strength were examined next. As a result, as described above, we found that it is necessary to form fine precipitates (less than 20 nm in size) and to increase the proportion of fine precipitates (less than 20 nm in size) to provide a high-strength steel sheet. Precipitates having a size of not less than 20 nm may result in low strength because they have little effect on inhibiting movement of dislocations and cannot therefore sufficiently harden ferrite. Accordingly, the size of the precipitates is preferably less than 20 nm. Fine precipitates having a size of less than 20 nm are achieved if the steel contains titanium and vanadium. Titanium and vanadium form carbides independently or together. Although the reason is unclear, we found that these precipitates remain fine stably at elevated temperatures within our range of coiling temperature for an extended period of time.
In the high-strength steel sheet, the precipitates containing titanium and/or vanadium form in ferrite mainly as carbides. This is probably because the solid solubility limit of carbon in ferrite is lower than that in austenite and supersaturated carbon tends to precipitate in ferrite as carbides. These precipitates harden (strengthen) ferrite, which is soft, thus achieving a TS of 980 MPa or more.
Therefore, of the hot-rolled steel sheets produced in the above experiment, those having a hardness difference (HVα−HVS) of −300 to 300 and a volume fraction of ferrite of 80% to 98% were examined for the amounts of titanium and vanadium contained in precipitates having a size of less than 20 nm.
According to
Accordingly, the structure includes 80% to 98% by volume of ferrite, the sum of the amounts of titanium and vanadium contained in precipitates having a size of less than 20 nm is 0.150% or more, and the difference (HVα−HVS) between the hardness of the ferrite phase (HVα) and the hardness of the second phase (HVS) is −300 to 300.
According to
Next, the reasons for the limitations on the chemical composition (composition) of the steel will be described.
Carbon is an element that forms carbides with titanium and vanadium to precipitate in ferrite, thus contributing to strengthening of the steel sheet. The amount of carbon needs to be 0.08% by mass or more to achieve a TS of 980 MPa or more. On the other hand, if the amount of carbon exceeds 0.20% by mass, the precipitates become coarse, thus decreasing the stretch flangeability. Accordingly, the amount of carbon is 0.08% to 0.20% by mass, preferably 0.09% to 0.18% by mass.
Silicon is an element that contributes to facilitation of ferrite transformation and solid-solution strengthening. Therefore, the amount of silicon is 0.2% by mass. However, if the amount thereof exceeds 1.0% by mass, the surface properties of the steel sheet deteriorate noticeably, thus decreasing corrosion resistance. Therefore, the upper limit of the amount of silicon is 1.0% by mass. Accordingly, the amount of silicon is 0.2% to 1.0% by mass, preferably 0.3% to 0.9% by mass.
Manganese is an element that contributes to solid-solution strengthening. However, if the amount thereof falls below 0.5% by mass, a TS of 980 MPa or more is not achieved. On the other hand, if the amount thereof exceeds 2.5% by mass, it noticeably decreases weldability. Accordingly, the amount of manganese is 0.5% to 2.5% by mass, preferably 0.5% to 2.0% by mass, and still more preferably, 0.8% to 2.0% by mass.
Phosphorus segregates at prior-austenite grain boundaries, thus degrading low-temperature toughness and decreasing workability. Accordingly, it is preferable to minimize the amount of phosphorus. Therefore, the amount of phosphorus is 0.04% by mass or less.
If sulfur segregates at prior-austenite grain boundaries or precipitates as MnS in large amounts, it decreases the low-temperature toughness and also noticeably decreases the stretch flangeability irrespective of whether working is carried out or not. Accordingly, it is preferable to minimize the amount of sulfur. Therefore, the amount of sulfur is 0.005% by mass or less.
Aluminum, which is added to the steel as a deoxidizing agent, is an element effective in improving the cleanliness of the steel. To achieve this effect, the steel preferably contains 0.001% by mass or more of aluminum. However, if the amount thereof exceeds 0.05% by mass, large amounts of inclusions form, thus causing defects in the steel sheet. Therefore, the amount of aluminum is 0.05% by mass or less. More preferably, the amount of aluminum is 0.01% to 0.04% by mass.
Titanium is an element of great importance for precipitation strengthening of ferrite. If the amount thereof falls below 0.07% by mass, it is difficult to ensure the necessary strength. On the other hand, if the amount thereof exceeds 0.20% by mass, the effect thereof is saturated, only ending up increasing the cost. Accordingly, the amount of titanium is 0.07% to 0.20% by mass, preferably 0.08% to 0.18% by mass.
Vanadium is an element that contributes to increased strength by precipitation strengthening or solid-solution strengthening and, along with titanium, described above, is an important requirement for achieving our advantages. An appropriate amount of vanadium contained together with titanium tends to precipitate as fine titanium-vanadium carbides having a grain size of less than 20 nm and, unlike molybdenum, does not decrease the corrosion resistance after coating. In addition, vanadium is less costly than molybdenum. If the amount of vanadium falls below 0.20% by mass, the above effect provided by containing it is insufficient. On the other hand, if the amount of vanadium exceeds 0.80% by mass, the effect thereof is saturated, only ending up increasing the cost. Accordingly, the amount of vanadium is 0.20% to 0.80% by mass, preferably 0.25% to 0.60% by mass.
The steel achieves the intended properties by containing the elements described above, although in addition to the above elements contained, it may further contain one or more of 0.01% to 1.0% by mass of chromium, 0.005% to 1.0% by mass of tungsten, and 0.0005% to 0.05% by mass of zirconium for the following reasons.
Chromium, tungsten, and zirconium serve to strengthen ferrite by forming precipitates or in a solid solution state, as does vanadium. If the amount of chromium falls below 0.01% by mass, the amount of tungsten falls below 0.005% by mass, or the amount of zirconium falls below 0.0005% by mass, they hardly contribute to increased strength. On the other hand, if the amount of chromium exceeds 1.0% by mass, the amount of tungsten exceeds 1.0% by mass, or the amount of zirconium exceeds 0.05% by mass, the workability deteriorates. Accordingly, if one or more of chromium, tungsten, zirconium are contained, the chromium content is 0.01% to 1.0% by mass, the tungsten content is 0.005% to 1.0% by mass, and the zirconium content is 0.0005% to 0.05% by mass. Preferably, the chromium content is 0.1% to 0.8% by mass, the tungsten content is 0.01% to 0.8% by mass, and the zirconium content is 0.001% to 0.04% by mass.
The balance other than above is iron and incidental impurities. An example of an incidental impurity is oxygen, which forms nonmetallic inclusions that adversely affect the quality. Therefore, the amount thereof is preferably reduced to 0.003% by mass or less. The steel may also contain copper, nickel, tin, and antimony in an amount of 0.1% by mass or less as trace elements that do not impair the advantageous effects.
Next, the structure of the high-strength steel sheet invention will be described. 80% to 98% of ferrite and second phase
To improve the stretch flangeability after working, it is probably effective that the primary phase be ferrite, which has low dislocation density, and the second phase be distributed in an island pattern in the steel sheet. As described above, the volume fraction of ferrite needs to be 80% to 98% for improved stretch flangeability after working In addition to the experimental results described above, if the volume fraction of ferrite falls below 80%, the stretch flangeability after working (λ10) and elongation (El) decrease probably because voids formed at interfaces between ferrite phases and second phases tend to be joined together during working On the other hand, if the volume fraction of ferrite exceeds 98%, although the reason is unclear, the stretch flangeability after working does not improve probably because numerous voids are formed at interfaces between the ferrite phases. Accordingly, the volume fraction of ferrite is 80% to 98%, preferably 85% to 95%.
The second phase, on the other hand, is preferably bainite phase or martensite phase. In addition, it is effective in view of stretch flangeability that the second phase be distributed in an island pattern in the steel sheet.
If the volume fraction of the second phase falls below 2%, the stretch flangeability might not improve because the amount of second phase is insufficient. On the other hand, if the volume fraction exceeds 20%, second phases are joined together during deformation of the steel sheet because the amount of second phase is excessive, which might decrease the stretch flangeability after working (λ10) and elongation (El). Accordingly, it is more preferable that the volume fraction of ferrite be 2% to 20%.
The volume fractions of ferrite and the second phase are determined by developing a cross sectional microstructure parallel to a rolling direction with 3% natal, examining the microstructure at a position one-fourth of the thickness using a scanning electron microscope (SEM) at a magnification of 1,500×, and measuring the area fractions of ferrite and the second phase as the volume fractions using the image processing software “Particle Analysis II” manufactured by Sumitomo Metal Technology Inc.
Sum of amounts of titanium and vanadium contained in precipitates having size of less than 20 nm is 0.150% by mass or more (where the amounts of titanium and vanadium are the respective concentrations based on 100% by mass of the total composition of the steel)
As described above, the sum of the amounts of titanium and vanadium contained in precipitates having a size of less than 20 nm is 0.150% by mass or more. There is no particular upper limit, although if the sum of the amounts of titanium and vanadium exceeds 1.0% by mass, the steel sheet fractures in a brittle manner and cannot therefore achieve the target properties, although the reason is unclear. Precipitates and/or inclusions are collectively referred to as “precipitates etc.”
The amounts of titanium and vanadium contained in precipitates having a size of less than 20 nm can be examined by the following method.
After a predetermined amount of sample is electrolyzed in an electrolytic solution, the sample piece is removed from the electrolytic solution and is immersed in a solution having dispersing ability. Precipitates contained in the solution are then filtered through a filter having a pore size of 20 nm. The precipitates passing through the filter having a pore size of 20 nm together with the filtrate have a size of less than 20 nm. After filtration, the filtrate is subjected to an analysis appropriately selected from, for example, inductively coupled plasma (ICP) emission spectrometry, ICP mass spectrometry, and atomic absorption spectrometry to determine the amounts in the precipitates having a size of less than 20 nm. Difference (HVα−HVS) between hardness (HVα) of ferrite phase and hardness (HVS) of second phase is −300 to 300
As described above, the difference (HVα−HVS) between the hardness (HVα) of the ferrite phase and the hardness (HVS) of the second phase is −300 to 300. If the hardness difference falls below −300 or exceeds 300, the required stretch flangeability after working is not achieved because more cracks occur at interfaces between ferrite phases and second phases due to the large difference in strain between the ferrite phases and the second phases after working. The hardness difference is preferably of smaller absolute value, preferably, −250 to 250.
Next, a method for manufacturing the high-strength steel sheet will be described.
The steel sheet is manufactured by, for example, heating a steel slab adjusted to the above ranges of chemical composition to a temperature of 1,150° C. to 1,350° C., hot-rolling the steel slab at a finish rolling temperature of 850° C. to 1,000° C., subjecting the steel sheet to first cooling to a temperature of 650° C. to lower than 800° C. at an average cooling rate of 30° C./s or higher, cooling the steel sheet with air for one to less than five seconds, subjecting the steel sheet to second cooling at a cooling rate of 20° C./s or higher, and coiling the steel sheet at a temperature of higher than 200° C. to 550° C. such that inequality (1) is satisfied:
T1≦0.06×T2+764 inequality (1)
wherein T1 is the first cooling stop temperature (° C.) and T2 is the coiling temperature (° C.).
These conditions will now be described in detail.
The carbide-forming elements, such as titanium and vanadium, are mostly present as carbides in the steel slab. To precipitate carbides in ferrite after hot rolling as intended, carbides precipitated before hot rolling need to be dissolved. This requires heating at 1,150° C. or higher. On the other hand, the heating temperature is 1,350° C. or lower because if the steel slab is heated above 1,350° C., the crystal grains become extremely coarse, thus degrading the stretch flangeability after working and the ductility. Accordingly, the slab heating temperature is 1,150° C. to 1,350° C., more preferably 1,170° C. to 1,260° C.
The steel slab after working is hot-rolled at a finish rolling temperature, which is the hot rolling termination temperature, of 850° C. to 1,000° C. If the finish rolling temperature falls below 850° C., an extended ferrite structure is formed because the steel slab is rolled in the ferrite+austenite region, thus degrading the stretch flangeability and the ductility. On the other hand, if the finish rolling temperature exceeds 1,000° C., a TS of 980 MPa is not achieved because the ferrite grains become coarse. Accordingly, the finish rolling is performed at a finish rolling temperature of 850° C. to 1,000° C.
More preferably, the finish rolling temperature is 870° C. to 960° C.
After the hot rolling, the steel sheet needs to be cooled from the finish rolling temperature to a cooling temperature of 650° C. to lower than 800° C. at an average cooling rate of 30° C./s or higher. If the cooling stop temperature is not lower than 800° C., the volume fraction of ferrite does not reach 80% because nucleation does not tend to occur, which makes it impossible to provide the intended precipitation state of precipitates containing titanium and/or vanadium. If the cooling stop temperature falls below 650° C., the volume fraction of ferrite does not reach 80% because the diffusion rates of carbon and titanium decrease, which makes it impossible to provide the intended precipitation state of precipitates containing titanium and/or vanadium. Accordingly, the cooling stop temperature is 650° C. to lower than 800° C. In addition, if the average cooling rate from the finish rolling temperature to the cooling stop temperature falls below 30° C./s, the stretch flangeability after working and the ductility deteriorate because pearlite forms. The upper limit of the cooling rate is preferably, but not limited to, about 300° C./s to accurately stop the cooling within the above range of cooling stop temperature.
After the first cooling, the cooling is stopped to allow the steel sheet to be cooled with air for one to less than five seconds. If the air cooling time falls below one second, the volume fraction of ferrite does not reach 80%; if the air cooling time exceeds more than five seconds, the stretch flangeability and the ductility deteriorate because pearlite forms. The cooling rate during the air cooling is about 15° C./s or lower.
After the air cooling, second cooling is performed to a coiling temperature of higher than 200° C. to 550° C. at an average cooling rate of 20° C./s or higher. The average cooling rate is 20° C./s or higher, preferably 50° C./s or higher, because pearlite forms during the cooling if the cooling rate falls below 20° C./s. The upper limit of the cooling rate is preferably, but not limited to, about 300° C./s to accurately stop the cooling within the above range of coiling temperature.
In addition, if the coiling temperature is not higher than 200° C., the steel sheet has a poor shape. On the other hand, if the coiling temperature is higher than 550° C., the stretch flangeability deteriorates because pearlite forms. Moreover, the hardness difference could be higher than 300. Preferably, the coiling temperature is 400° C. to 520° C.
T1≦0.06×T2+764 wherein T1 is the first cooling stop temperature (° C.) and T2 is the coiling temperature (° C.)
During the air cooling after the first cooling, fine precipitates form in ferrite. This allows most of the ferrite phase to be precipitation-strengthened. The hardness of the precipitation-strengthened ferrite phase depends on the temperature at which the precipitates form, that is, the first cooling stop temperature. The hardness of the second phase, on the other hand, depends on the transformation temperature, that is, the coiling temperature. As a result of various studies, it has turned out that the hardness difference is −300 to 300 if, letting the first cooling stop temperature be T1 (° C.) and the coiling temperature be T2 (° C.), T1≦0.06×T2+764 is satisfied. For T1>0.06×T2+764, the hardness difference falls below −300 because the ferrite phase has low hardness and the second phase has high hardness.
Thus, a high-strength steel sheet having excellent stretch flangeability after working is provided. Steel sheets include surface-treated or surface-coated steel sheets. In particular, a steel sheet is suitable for use as a hot-dip galvanized steel sheet by forming a hot-dip galvanized coating. That is, a steel sheet which has good workability can maintain its good workability after a hot-dip galvanized coating is formed. The term “hot-dip galvanizing” refers to hot-dip coating with zinc or a zinc-based alloy (i.e., containing about 90% or more of zinc) and includes coating with an alloy containing an alloying element other than zinc, such as aluminum or chromium. In addition, alloying treatment may be performed after the hot-dip galvanizing.
In addition, there is no particular limitation on the method for preparing the steel, and all known methods for preparation can be applied. An example of a preferred method for preparation is one in which the steel is prepared in, for example, a converter or electric furnace and is subjected to secondary refining in a vacuum degassing furnace. The casting method is preferably continuous casting in terms of productivity and quality. In addition, the advantages are not affected even if the steel is subjected to direct rolling, that is, even if the steel is directly hot-rolled immediately after casting or after the steel is heated to add more heat. Furthermore, a hot-rolled sheet after rough rolling may be heated before finish rolling, and the advantages are not impaired even if continuous hot rolling is performed by joining rolled sheets together after rough rolling or even if heating of rolled sheets and continuous rolling are simultaneously performed.
Steels of the compositions shown in Table 1 were prepared in a converter and were continuously cast into steel slabs. These steel slabs were then heated, hot-rolled, cooled, and coiled under the conditions shown in Tables 2 and 3 to produce hot-rolled steel sheets having a thickness of 2.0 mm. The coiling temperature shown in Tables 2 and 3 is an average of coiling temperatures measured longitudinally in the center of the steel strip across the width.
The resulting hot-rolled steel sheets were examined for the amounts of titanium and vanadium contained in precipitates having a size of less than 20 nm by the following method.
Measurement of Amounts of Titanium and Vanadium Contained in Precipitates Having Size of Less than 20 nm
The hot-rolled steel sheets thus produced were cut to an appropriate size, and about 0.2 g was electrolyzed with constant current at a current density of 20 mA/cm2 in a 10% AA electrolytic solution (10% by volume acetylacetone-1% by mass tetramethyl-ammonium chloride-methanol).
After the electrolysis, the sample piece, which had precipitates thereon, was removed from the electrolytic solution, was immersed in a sodium hexametaphosphate aqueous solution (500 mg/L) (hereinafter referred to as “SHMP aqueous solution”), and was subjected to ultrasonic vibration to release the precipitates from the sample piece into the SHMP aqueous solution. The SHMP aqueous solution containing the precipitates was then filtered through a filter having a pore size of 20 nm, and the filtrate after the filtration was analyzed using an ICP emission spectrometer to measure the absolute amounts of titanium and vanadium in the filtrate. The absolute amounts of titanium and vanadium were then divided by the electrolyzed weight to determine the amounts of titanium and vanadium contained in precipitates having a size of less than 20 nm (% by mass based on 100% by mass of the total composition of the sample). The electrolyzed weight was determined by measuring the weight of the sample after the release of the precipitates and subtracting it from the weight of the sample before the electrolysis.
In addition, JIS No. 5 tensile specimens (parallel to the rolling direction), hole expanding specimens, and a sample for structural examination were taken from each coil at a position 30 m from an end thereof in the center across the width, and the tensile strength TS, the elongation El, the stretch flangeability after working λ10, and the hardness difference HVα−HVS were determined and evaluated by the following methods.
The tensile strength (TS) and the elongation (El) were determined by taking three JIS No. 5 tensile specimens such that the tensile direction was the rolling direction and carrying out a tensile test by a method complying with JIS Z 2241.
λ10 was determined by taking three specimens for a hole expanding test, rolling the specimens to an elongation of 10%, carrying out a hole expanding test according to Japan Iron and Steel Federation Standard JFS T1001, and calculating the average of the three pieces.
The tester used for a Vickers hardness test was one complying with JIS B7725. A sample for structural examination was taken, the structure thereof was developed with a 3% natal solution in a cross section parallel to the rolling direction, and dents were made on ferrite grains and second phases at a position one-fourth of the thickness at a test load of 3 g.
The hardness was calculated from the diagonal length of the dents using the Vickers hardness test calculation formula in JIS Z2244. The hardnesses of 30 ferrite grains and 30 second phases were measured, and the averages thereof were used as the hardness (HVα) of the ferrite phase and the hardness (HVS) of the second phase to determine the hardness difference (HVα−HVS).
In addition, the volume fractions of ferrite and the second phase were determined by developing the cross sectional microstructure parallel to the rolling direction with 3% natal, examining the microstructure at a position one-fourth of the thickness using a scanning electron microscope (SEM) at a magnification of 1,500×, and measuring the area fractions of ferrite and the second phase as the respective volume fractions using the image processing software “Particle Analysis II” manufactured by Sumitomo Metal Technology Inc.
The results thus obtained are shown in Tables 2 and 3 together with the manufacturing conditions.
According to Table 2, high-strength steel sheets having excellent stretch flangeability after working with a TS (strength) of 980 MPa or more and a λ10 of 40% or more were provided in the Examples. In addition, the El (elongation) was sufficient, namely, 15% or more.
According to Table 3, in contrast, the Comparative Examples were poor in one or both of TS and λ10.
Steels of the compositions shown in Table 4 were prepared in a converter and were continuously cast into steel slabs. These steel slabs were then heated, hot-rolled, cooled, and coiled under the conditions shown in Table 5 to produce hot-rolled steel sheets having a thickness of 2.0 mm. The coiling temperature shown in Table 5 is an average of coiling temperatures measured longitudinally in the center of the steel strip across the width.
The resulting hot-rolled steel sheets were examined for the amounts of titanium and vanadium contained in precipitates having a size of less than 20 nm by the same method as in Example 1. In addition, the tensile strength TS, the elongation El, the stretch flangeability after working λ10, and the hardness difference HVα−HVS were determined and evaluated by the same methods as in Example 1.
The results thus obtained are shown in Table 5 together with the manufacturing conditions.
According to Table 5, high-strength steel sheets having excellent stretch flangeability after working with a TS of 980 MPa or more and a λ10 of 40% or more were provided in the Examples. Table 5 also shows that the steels containing chromium, tungsten, or zirconium in Example 2 had a higher TS than the steels in Example 1 based on the same compositions.
A steel sheet has high strength and excellent stretch flangeability after working and is therefore best suited to, for example, parts requiring ductility and stretch flangeability, such as frames for automobiles and trucks.
| Number | Date | Country | Kind |
|---|---|---|---|
| 2009-163309 | Jul 2009 | JP | national |
This is a §371 of International Application No. PCT/JP2010/061363, with an international filing date of Jun. 29, 2010 (WO 2011/004779 A1, published Jan. 13, 2011), which is based on Japanese Patent Application No. 2009-163309, filed Jul. 10, 2009, the subject matter of which is incorporated by reference.
| Filing Document | Filing Date | Country | Kind | 371c Date |
|---|---|---|---|---|
| PCT/JP2010/061363 | 6/29/2010 | WO | 00 | 1/3/2012 |
