2015-MSEA-linear friction welded joints betweenTC11 and TC17 dissimilar titanium alloys-线摩擦焊

Strain hardening behavior of linear friction welded joints between

TC11and TC17dissimilar titanium alloys

Pengkang Zhao,Li Fu n

State Key Laboratory of Solidi?cation Processing,Shaanxi Key Laboratory of Friction Welding Technologies,Northwestern Polytechnical University,

Xi’an710072,Shaanxi,PR China

a r t i c l e i n f o

Article history:

Received10September2014

Received in revised form

16October2014

Accepted17October2014

Available online23October2014

Keywords:

Linear friction welding(LFW)

Dissimilar titanium alloys

Strain hardening behavior

Strain rate sensitivity

a b s t r a c t

The in?uence of strain rate on the tensile properties and its distribution of linear friction welded

(LFWed)dissimilar joints between Ti–6.5Al–3.5Mo–1.5Zr–0.3Si(TC11)and Ti–4Mo–4Cr–5Al–2Sn–2Zr

(TC17)titanium alloys were studied in this paper.Furthermore,strain hardening behavior,strain rate

sensitivity and fracture characteristic of the LFWed joints have been evaluated.It was found that a great

deal of ultra-?ne grains appear on the TC11side of weld zone(WZ).The microstructure on the TC17side

of WZ is composed of coarsenedβphase,a lot of slip lines and dislocation networks within the

boundaries ofβgrains generate under high temperature deformation by transmission electron

microscope(TEM).A distinctive asymmetrical hardness pro?le is observed across the joint,with higher

hardness on the TC11side of WZ and lower hardness on the TC17side of WZ,respectively.While the

yield strength(YS),ultimate tensile strength(UTS)of the joint increase,both hardening capacity and

strain hardening exponent n-value decrease with increasing strain rate,meanwhile,the strain-hardening

rateθincreases at a given true stress.Strain rate sensitivity of the welding joint decreases with

increasing plastic strain.Moreover,the fracture location of the LFWed joints between TC11and TC17

titanium alloys almost locate at the regions with lower hardness.Additionally,ductile fractures and a

mixed cleavage fractures appear respectively at the center and edge area of the LFWed joints.

&2014Elsevier B.V.All rights reserved.

1.Introduction

Titanium and its alloys have been successfully and increasingly

used in the aerospace industrial area for their unique properties,

such as low density,high speci?c strength,wide operating

temperature range and superior corrosion-resistant ability[1–4].

At high temperatures,the metal reacts strongly with atmospheric

gases such as oxygen and nitrogen,thus the welding in air would

make the joint completely brittle.Therefore,only in a vacuum or a

protective atmosphere are Ti and its alloys weldable.The tradi-

tional fusion welding usually exist poor shielding of the welding

zone or impure shielding gas during the welding process,which

could lead to serious contamination[5].Therefore,the solidi?ca-

tion problems appear,e.g.porosity,hot cracking,segregation,etc.

To overcome these problems,linear friction welding(LFW)is

considered to be an ideal process to join titanium and its alloys.

LFW is a solid state process for joining materials together

through intimate contact of a plasticized interface,which is

generated by frictional heat produced as one component is moved

relatively to another under pressure[6–8].It is a complicated and

quick thermo-mechanically coupled physical process,which is

suitable for materials with low thermal conductivity and high

temperature mechanical properties[9].Therefore,the process is

considered to be particularly appropriate for joining of titanium

and nickel alloys[10–12].The development of LFW has been

driven by the aeroengine manufacturing industry to fabricate

integrally bladed disks(blisks)giving light weight and improved

performance over the existing slotted blade/disk assemblies[8].

There are some research works related with LFW of titanium alloys

in recent years.Vairis and Frost[13,14]systematically analyzed the

change laws in different phases of the Ti–6Al–4V alloy LFWed

joints at variable frequencies and amplitudes of oscillation.The

process is divided into four distinct phases:in the?rst phase,the

two materials are brought in contact under pressure and heat is

generated from solid friction;in the transition phase,heat affected

zone expands and the true contact area is considered to be100%of

the cross-sectional area,and the soft plasticized layer is no longer

able to support the axial load;in the equilibrium phase,axial

shortening increases sharply and heat is conducted away from the

interface and a plastic zone develops;in the deceleration phase,

the relative motion is stopped abruptly and forging pressure is

applied to consolidate the weld.Karadge et al.[15]examined the

microstructure and texture development in as-welded and post

weld heat treated Ti–6Al–4V LFWed joints.Frankel et al.[16]

Contents lists available at ScienceDirect

journal homepage:https://www.sodocs.net/doc/4212901315.html,/locate/msea

Materials Science&Engineering A

https://www.sodocs.net/doc/4212901315.html,/10.1016/j.msea.2014.10.044

0921-5093/&2014Elsevier B.V.All rights

reserved.

n Corresponding author.

E-mail address:fuli@https://www.sodocs.net/doc/4212901315.html,(L.Fu).

Materials Science&Engineering A621(2015)149–156

compared the residual stresses between Ti –6Al –4V and Ti –6Al –2Sn –4Zr –2Mo LFW.Romero et al.[6]examined the effect of the forging pressure on the microstructure and residual stress devel-opment in Ti –6Al –4V LFW.Refs.[17–19]investigated the micro-structure and mechanical properties of LFWed joints of Ti –6Al –4V alloy,such as impact toughness and fracture characteristics.

The strength,ductility,toughness and deformability of materi-als are intimately related to strain hardening characteristics [20].For this reason,many investigations have been carried out on the strain hardening behavior and physical mechanism of conven-tional metallic materials [21,22].Hitherto many studies have been reported on the strain hardening behavior of Ti alloys.For example,Bystrzanowski et al.[23]investigated the tensile ?ow behavior of Ti –46Al –9Nb sheet material and observed only stage III strain hardening at high temperatures.Honarmandi and Aghaie-Khafri [24]studied the strain hardening behavior of Ti –6Al –4V and TiAlx alloys,respectively,by means of compression testing at high temperatures and observed different stages of strain hardening.In spite of many studies focused on the strain hardening behavior of titanium alloys as well as the strain hard-ening behavior of welded joints,there were few reports about the dynamic mechanical behavior of LFWed dissimilar titanium alloy joints until now.However,for the reliable design of the gas turbine structural components,it was very important to understand the mechanical behavior of LFWed joints as well as the strain rate effect on it.Therefore,this study was aimed at evaluating the strain rate effects on the mechanical properties,deformation and fracture behavior of LFWed joints with TC11and TC17dissimilar alloys.Due to the different stress and environmental status of the blade and disk,for example,the disk bears large tensile stress on the low temperature and the blade bears small stress on the high temperature,therefore,dual alloy (TC11as blade and TC17as disk)–dual property blisk can play a greater extent their excellent performance,and work in a larger temperature gradient and stress gradient conditions.

2.Materials and methods

The materials used in the present study are forged TC11and TC17titanium alloys,and their chemical compositions were listed in Table 1.Both alloys were machined into the plates with a dimension of 130mm ?75mm ?20mm,and then mechanically and chemically cleaned before welding.The LFW machine was developed by Beijing Aeronautical Manufacturing Technology Research Institute (China)and was carried out with oscillation frequency of 40Hz,amplitude of 3mm,friction pressure of 50MPa,and friction time of 3.6s.

Metallographic samples of the welded joints cut perpendicular to the welding direction were prepared and examined via optical microscopy (OM),scanning electron microscopy (SEM)and trans-mission electron microscope (TEM).Vickers microhardness was determined using a load of 500g and a dwell time of 15s.All the microhardness values presented in this study were an average of three series of values taken on the same specimen.The center point of the WZ was determined carefully after observing the weld geometry under microscope and all the indentations were

adequately spaced to avoid any potential effect of strain ?eld caused by adjacent indentations.

Tensile tests were performed using ASTM-E8M subsized sam-ples on a fully computerized tensile testing machine at room temperature and strain rates from 10à5to 10à2s à1.Subsized tensile specimens of 100mm long with a gauge length of 25mm (or a parallel length of 32mm)and gauge width of 6mm were machined perpendicularly to the welding direction using electro-discharge machining (EDM).The gauge area was ground up to #1000SiC papers to remove the EDM cutting marks and to achieve a smooth and consistent surface.Three specimens in each case were tested to check the reproducibility of the test data.The 0.2%offset YS,UTS,ductility and the work hardening properties were evaluated.Fracture morphologies after tensile testing were exam-ined using SEM to identify the fracture mechanisms.

3.Results and discussion 3.1.Microstructure

The microstructures of the base metals (BM)are shown in Fig.1.It is seen that the BM consists of αtβphases.The microstructure of TC11alloy is composed of equiaxed prior-αphase and intergranular transformed βphase (mixture of lamellar αand βphases).The volume fraction of βphase is about 47.4%[25].TC17alloy is rich in βphase and is composed of basket-weave microstructure,and αphase precipitates uniformly within grains [26].After LFW,a remarkable change of microstructure occurs in the WZ and thermo-mechanically affected zone (TMAZ)as shown in Fig.2(a)-(d).It can be clearly seen that the welding interface between the TC11and TC17alloys.The microstructures of WZ between TC11and TC17alloys are different each other.The microstructure on the TC11side of WZ consists of acicular and ?ne martensites α0and α″during the thermo –mechanical proces-sing due to high thermal conductivity and fast cooling rate and a relatively short dynamic recrystallization (DRX)period [8,27,28],as shown in Fig.2(b)and (d).In contrast,the microstructure on the TC17side of WZ is composed of coarsened βphase (Fig.2b and c),which is attributed to more β-stabilizing alloying elements exist-ing in Table 1and long DRX period with low thermal conductivity.The results lead to the presence of a soft zone [29–31].The percentage of DRX increases with temperature above 10001C [32].For further to investigate the microstructural features in the WZ of LFWed joints,TEM test method was applied on the TC11and TC17sides of WZ as shown in Fig.2(e)and (f).Lots of slip lines and dislocation networks within the boundaries of βgrains are generated under high temperature deformation on the TC17side of WZ during the LFW process.The βgrain of the body-centered cubic (BCC)crystal structure is shown by the selected-area diffraction pattern (SADP)with a typical diffraction pattern of zone axis [001].Due to the high stacking fault energy (SFC)of titanium alloys,dislocations are hard to break down [33].During the deformation,the dislocations are tangled with the help of crossing and climbing,more dislocations gather and high-angle subgrain boundaries appear.On the TC11side of WZ,the marten-site α0of the hexagonal close packed (HCP)crystal with the SADP forms during the fast cooling and the certain dislocation density occurs due to the thermoplastic deformation [33–35].The micro-structures of TMAZ on both TC11and TC17sides become elongated along the ?ow direction of plasticized materials,which are almost parallel to the weld line and the streamline (Fig.2c and d).The microstructure of the joint at the edge zone is similar with the center zone.However,the width of the edge zone is wider than the central region due to more energy stored at the edge zone by the heat re ?ux of the ?ash after welding.The reason is that the

Table 1

Chemical composition (wt%)of TC11and TC17titanium alloys.elements Al Mo Cr Si Sn Zr Ti

TC11 5.8–7.0 2.8–3.8–

0.2–0.4–

1.0–

2.0Allowance TC17

4.5–

5.5

3.5–

4.5

3.5–

4.5

–

1.5–

2.5

1.5–

2.5

Allowance

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150

heat loss by radiation and convection is less than conductivity.The detailed analysis has been described in our previous paper [8].3.2.Microhardness

Fig.3shows Vickers microhardness pro ?les along the center and edge area of the dissimilar LFWed joints between TC11and TC17alloys.It is seen that distinctive asymmetrical hardness pro ?les across the dissimilar weld are present with an average hardness value of $360HV for TC11BM and $390HV for TC17BM,https://www.sodocs.net/doc/4212901315.html,pared with the TC11BM,the higher hard-ness in the TC17BM is related to the overall higher alloying elements in the TC17alloy (Table 1)and basket-weave micro-structure (Fig.1b)where αphase precipitates uniformly within grains,offering a strong resistance to the motion of dislocations during plastic deformation.In the center zone of the joint,the appreciably higher hardness value on the TC11side of WZ which is obviously attributed to the grain re ?nement and ?ne

martensites

Fig.1.Microstructures of (a)TC11BM and (b)TC17

BM.

Fig.2.Microstructure of the LFWed joints between TC11and TC17alloys,(a)overall view of the cross section,(b)welding joint at higher magni ?cation,(c)TC17side of WZ,(d)TC11side of WZ,(e)TEM micrographs showing selected-area diffraction pattern (SADP)of βon the TC17side of WZ,(f)TEM micrographs showing the SADP of αon the TC11side of WZ.

P.Zhao,L.Fu /Materials Science &Engineering A 621(2015)149–156151

α0and α″,and lower hardness value on the TC17side of WZ,which is ascribed to relatively soft and coarse βphase as shown in Fig.2(b)and (c)[27,36].It is also observed that the hardness value declines gradually from the weld centerline to TC11BM due to dropping temperature and martensite from the welding line.However,the hardness of TC17side increases from the WZ boundary up to TC17BM with increasing distance,which can be explained by the reduction of coarse βphase through dropping temperature.The width of the joint in the edge is wider than the center zone (Figs.3and 4).The hardness in the TC17side of WZ is lower than the TC11BM,which can be ascribed to a longer time of heat treatment at the edge of the joint,more coarse βphase are formed.The phenomena can be also explained from the welding process on the basis of the simulation.The temperature evolution at the center and edge areas of the friction interface of TC11side is shown in the Fig.4.TC17side has the similar law.The temperature

of ?ash decreases more slowly than that of the interface center.More detailed results on the temperature evolution of the simula-tion has been reported in our earlier literature [8].3.3.Tensile properties

3.3.1.Effect of strain rate on the YS and UTS

Fig.5shows typical stress –strain curve of TC11and TC17BMs,and their dissimilar joints at a strain rate of 10à3s à1at room temperature.The smooth and continuous stress –strain curves occur on the BMs and joint [37].It is also seen from Fig.5that the TC11alloy is more ductile than the TC17alloy,despite its lower ?ow stress than that of TC17alloy.This is directly associated with the microstructure and grain morphology as shown in Fig.1.The lamellar microstructure is usually preferable for the strength,fracture toughness,fatigue crack propagation,and oxidation beha-vior,while the globular microstructure is better for the ductility and fatigue crack initiation [31,38,39].As seen from Fig.1,TC11alloy consists of more globular α,while TC17exhibits a lamellar microstructure as mentioned above.Therefore,the ductility of TC11alloy is higher than that of TC17alloy,and the strength of TC11alloy is lower than that of TC17alloy.

In the normal case,the strength of the BM is supposed to be higher than that of welded joint [40,41].However,a special or seemingly abnormal characteristic is observed in Fig.5.For example,the stress –strain curve of the LFWed joint lies in-between those of the two BMs of TC11and TC17alloys.Wen et al.[42]and Ma et al.[36]also found the similar phenomena on the LFWed joint of Ti –6Al –4V and Ti –6.5Al –3.5Mo –1.5Zr –0.3Si alloys.Fig.6shows the typical stress –strain curves tested under various strain rates at the different location of the LFWed joints with TC11and TC17alloys.As seen from Fig.6(a),the ?ow curves shift higher with increasing strain rate.Meanwhile,the lower strength and ductility happen at the edge area of the LFWed joints as shown in Fig.6(b).The phenomena correspond with the microstructure and the microhardness on the welding joint.More energy stored at the edge zone of the joint leads to the increasing width of coarse βphase zone and lower microhardeness on the TC17side of WZ compared with the TC11BM in Fig.3.This suggests a strong dependence of the ?ow behavior on the location during the LFW.In all the cases a small slope of the curves is present in the plastic range,which shows a relatively low strain-hardening rate in most titanium alloys [43].

Fig.7(a)gives the YS and UTS of TC11/TC17dissimilar joint under different tensile stain rate at the center zone of the joint at room temperature.As shown in Fig.7(a),the YS and UTS of the LFWed joint increase with the increasing of tensile strain rate,but the YS increase more quickly than the UTS.That suggests a

strong

Fig.3.Hardness pro ?le across the center and edge of the dissimilar welded joint between TC11and TC17

alloys.

Fig.4.Simulation temperature evolution at the center and edge of the friction interface on the TC11

side.Fig.5.Typical tensile stress –strain curve of TC11BM,TC17BM,and their joint,respectively,at a strain rate of 10à3s à1at room temperature.

P.Zhao,L.Fu /Materials Science &Engineering A 621(2015)149–156

152

strain rate dependence of both YS and UTS for LFWed joints with TC11and TC17alloys.The average YS of the LFWed joints increase from about 918MPa at a strain rate of 10à5s à1to about 1060MPa at a strain rate of 10à2s à1,and the corresponding average UTS also increase from about 1035MPa to about 1106MPa in the same strain range.The reason of strain rate dependent behavior can be ascribed to plastic deformation mechanism for dislocation slip at low strain rates and twinning at the high strain rate [44–47].Traces of plastic deformation occur during the yield process.Another reason for this is mainly determined by competing processes of strain hardening,strain rate of reinforcement and adiabatic tem-perature rise softening.The ?ow stress increases with the increas-ing of the strain rate,indicative of positive strain rate sensitivity.When the material happens plastic deformation,the dislocation rapidly proliferates and the density of the dislocation increases,the dislocation slips more and more dif ?cultly,which causes the strain hardening.At high strain rates,however,the plasticity deformation does not have enough time to proceed.So it shows lower plasticity [48].Fig.7(b)shows the effect of strain rate on the ductility of the welding joints at the center and edge zones.As seen from the ?gure,the ductility of the LFWed joints decline with the increasing of strain rate at the center area of the joints,and the ductility of the joints at edge area are lower than the center part.

3.3.2.Effect of strain rate on strain hardening behavior

The hardening capacity H C may be simply de ?ned as follows [49],

H C ?σUTS àσy σy ?σUTS

σy à1;e1T

where σy and σUTS are YS and UTS respectively.Fig.8shows the

hardening capacity of the dissimilar joint tested under various

strain rates at the different locations by Eq.(1).The results show that the hardening capacity of the joints decrease with increasing strain rate and the effect of the locations can be ignored.Based on Eq.(1),the hardening capacity of a material is related to its YS and UTS.As seen from Fig.7(a),the slope of the YS is slightly steeper than that of the UTS with the increasing of strain rate,therefore the H C decrease with increasing strain rates as shown in the Fig.8.For example,the YS increase from about 918MPa to about 1060MPa when the strain rate increase from 10à5s à1to 10à2s à1,and the corresponding value of H C decrease from 0.127to 0.043.The grain size and dislocation density of the material during plastic deforma-tion have important effects on the H C [49–52].

Fig.9shows the strain hardening exponent of the dissimilar joints with the strain rate by a modi ?ed relationship proposed

by

Fig.6.Tensile stress –strain curve of TC11/TC17dissimilar joints tested at (a)different strain rates at the center zone of the joints at room temperature,and (b)different locations at a constant strain rate of 10à3s à1

.

Fig.7.Effect of strain rate on (a)YS and UTS,(b)ductility of the dissimilar joints at room

temperature.

Fig.8.Effect of strain rate on the hardening capacity of the TC11/TC17dissimilar joints.

P.Zhao,L.Fu /Materials Science &Engineering A 621(2015)149–156153

Afrin et al.[49],σàσy ?K eεàεy Tn ;

e2T

where σy ,εy ,K and n are the YS,yield strain,constant and strain hardening exponent.In Eq.(2)the elastic component in both stress and strain is indeed excluded.It is seen that n-values decrease with the increasing of strain rate at room temperature.The phenomena can be explained on the basis of the following relationship between strain hardening exponent (n )and the strain

rate (_ε)[53],n ?n 0àblg _ε

;e3T

where n 0is a material constant,and b is the slope in the n vs.lg _ε

graph.Meanwhile,the n-value of the edge of the joint is very low,which can be attributed to the lower ductility and little strain-hardening.The change of strain hardening exponents with strain rates correspond well to that of hardening capacity (Fig.8).

Fig.10shows a typical Kocks –Mecking plot of strain-hardening rate (θ?d σ=d ε)versus true stress at the various strain rates for LFWed joint.No stage I hardening (depending on the crystal orientation)and stage II hardening (strain-hardening rate being constant)are not observed in the welded joint and only stage III hardening (strain-hardening rate decreasing almost linearly with increasing true stress)appears immediately after yielding.As can be seen from Fig.10,stage III is strongly strain-rate sensitive in welding joint.The strain-hardening rate θdecrease almost linearly with increasing ?ow stress,and the θincrease at a given true stress with increasing strain rate.This could be ascribed to the following

equation [22],θ?θo à

R d

_ε

1=q σ;e4T

where R d and q are temperature dependent constants,which are

independent of stress and strain rate,θis the strain-hardening rate in stage III,and θo is considered as a constant.It is clear that the strain-hardening rate θincrease with increasing strain rate.

3.3.3.Effect of strain rate on strain rate sensitivity

Strain rate sensitivity (SRS)is one of the key engineering parameters to accurately predict the deformation behavior of the materials during loading [54].The strain rate sensitivity of the ?ow stress is de ?ned as the following equation [55,56],m ??ln σ=?ln _ε

??log σ=?log _ε;e5T

where σand _ε

are the ?ow stress and the strain rate,respectively.A highly strain-rate sensitive material is expected to resist loca-lized deformation and hence may be ductile [57].The steady-state ?ow stress of the TC11/TC17welding joints at 1%,2%,3%and 5%plastic strain are plotted in logarithmic form as a function of the logarithmic form of the strain rate.As shown in Fig.11,the m value of the TC11/TC17welding joints at 1%,2%,3%and 5%plastic strain are 0.010,0.013,0.011and 0.009respectively.It is seen that the strain rate sensitivity m value of the welding joints decrease with the increasing of plastic strain [58].The reason for the strain rate sensitivity m decreasing with the increase of plastic strain can be explained by the increasing twin density on the microstructure and the competition between the rate of work hardening and the rate of thermal softening during deformation processes [59,60]

.

Fig.9.Effect of strain rate on the strain hardening exponent

n-value.

Fig.10.The strain-hardening rate vs.true stress at different strain rates at room

temperature.

Fig.11.Flow stress in logarithm vs.strain rate in logarithm at 1%,2%,3%and 5%

true strain at the center of the joint at room temperature.Strain rate sensitivity (m)is calculated from the

slope.

Fig.12.Fracture locations under various strain rates at the center and edge area of the joints.

P.Zhao,L.Fu /Materials Science &Engineering A 621(2015)149–156

154

3.4.Fracture morphology

On a macroscopic scale,the fracture locations between the center and edge area of the joints are shown in Fig.12.It shows that the LFWed joints in the center area always fail at the TC11BM and in the edge area fail on the TC17side of WZ.The fracture location of the LFWed joints almost locate at the lowest hardness regions shown in Fig.3.The reason can be explained from the microstructure and grain morphology at the center and edge areas of the LFWed joint.More detailed analysis has been discussed in Sections 3.2and 3.3.1.The fracture morphology of the tensile test specimens are characterized by using SEM.Fracture morphologies at the center area of the joints are similar under various strain rates and the strain rate of 10à3s à1is more commonly used in most cases,therefore,fracture morphologies in the center and edge area of LFWed joint at strain rate of 10à3s à1are presented in Fig.13.The fracture morphologies in the center area of the joint are characterized by the ductile fractures with a plenty of equiaxed and tearing dimples (Fig.13a and c).Fig.13(b)and (d)show quasi-cleavage and intergranular dimple fracture features with lots of cleavage steps,river patterns and tearing ridges at the edge area of the joint.As discussed above,the center area of the joints show better ductility than the edge area.

4.Conclusions

In summary,the following conclusions are reached:

1.On the TC11side of WZ,the microstructure consists of acicular and ?ne martensite,appreciably higher hardness value occurs;on the TC17side of WZ,the microstructure is composed of the coarsened βphase,and lower hardness value appears.

2.The stress –strain curve of the TC11/TC17LFWed joint lies in-between those of the two BMs.The TC11alloy is more ductile,despite it is lower ?ow stress than TC17alloy.The YS,UTS of the TC11/TC17LFWed joint increase and the ductility decline with the increasing of strain rate.

3.As the strain rate increases,the hardening capacity and strain hardening exponent decrease and strain-hardening rate θincreases at a given true stress,and θdecreases almost linearly with increasing ?ow stress.Meanwhile,the strain rate sensi-tivity m values decrease with increasing plastic strain.

4.The center area of the TC11/TC17LFWed joints always fail at the TC11BM,and fracture morphologies are ductile fracture with a plenty of equiaxed and tearing dimples.The edge area of the joints fail in WZ near the TC17side,and fracture morphologies show the quasi-cleavage and intergranular dimple fracture features.

Acknowledgments

This work was supported by the Project of Key areas of innovation team in Shaanxi Province (No.2014KCT-12),the Pro-gramme of Introducing Talents of Discipline to Universities (No.B08040)and Innovation Project of Shaanxi Province Overall Plan on Science and Technology (No.2012HBSZS021).References

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It Is Necessary To Clarify The Rights And Obligations Of The Parties, To Restrict Parties, And To Supervise Both Parties To Keep Their Promises And To Restrain The Act Of Reckless Repentance. 编订：XXXXXXXX 20XX年XX月XX日 中国总代理协议简易版

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所列的条款和条件，与卖方洽谈欲引进技术的价格及其他有关事项。兹同意下列条款：第二条定义２．１．本协议内所用词汇的意义，明确阐述如下：“佣金”系按本协议所列的条款和条件，由委托人按照６．１．条款支付给总代理人的佣金。“许可证协议”系指委托人与卖方所签订的技术转让或许可证协议，包括与技术有关的于任何时候所作的补充、修改和增补的技术，由卖方出售、转让该技术并向委托方予以报价。“价格”系指委托人为引进该项技术而支付给卖方的款额，包括许可证和特许权使用费及其他费用，由委托方向卖方支付的款额。２．２．各条款所列的标题仅为醒目而用，对本协议的解释无影响。 第三条总代理３．１．委托人指定其总

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0M-4 55 75 102.5 0.88 92.6 1480 2 7 2.2 Y250M-6 37 50 72 0.86 90.8 980 1.7 6.5 2 Y250M-8 30 40 63 0.8 90.5 740 1.8 6 2 外形及安装尺寸 安装尺寸 (mm) 外形尺寸(mm) 机座号 A B C D E F G H K M N P R S T AB AC AD HD HF L Y80 125 100 50 19 40 6 15.5 80 10 165 130 200 0 12 3.5 165 175 150 175 185 290 Y90S 140 100 56 24 50 8 20 90 10 165 130 200 0 12 3.5 180 195 160 195 195 315 Y90L 140 125 56 24 50 8 20 90 10 165 130 200 0 12 3.5 180 195 160 195 195 340 Y100L 160 140 70 28 60 8 24 100 12 215 180 250 0 15 4.0 205 215 180 245 245 380 Y112M 190 140 70 28 60 8 24 112 12 215 180 250 0 15 4.0 245 240 190 265 265 400 Y132S 216 140 89 38 80 10 33 132 12 265 230 300 0 15 4.0 280 275 210 315 315 475 Y132M 216 178 89 38 80 10 33 132 12 265 230 300 0 15 4.0 280 275 210 315 315 515 Y160M 245 210 108 42 110 12 37 160 15 300 250 350 0 19 5.0 325 325 255 385 385 600 Y160L 245 254 108 42 110 12 37 160 15 300 250 350 0 19 5.00 325 325 255 385 385 645 Y180M 279 241 121 48 110 14 42 180 15 300 250 350 0 19 5.0 355 360 285 430 430 670 Y180L 279 279 121 48 110 14 42 180 15 300 250 350 0 19 5.0 355 360 285 430 430 710 Y200L 318 305 133 55 110 16 49 200 19 350 300 400 0 19 5.0 395 400 310 475 475 775 Y225S 356 286 149 60 110 16 49 225 19 400 350 450 0 19 5.0 435 435 345 520 520 820 Y225M 356 311 149 55 110 16 49 225 19 400 350 450 0 19 5.0 435 435 345 520 520 815