t14-VELOCITY MEASUREMENTS IN CAVITATING FLOWS USING FAST X-RAY IMAGING

HALSEY TAYLOR OWNERS MANUALUSES HFC-134A REFRIGERANTFIG. 1253, 472, 30 - SEE FIG.5 5, 697321C (7/98)F IG . 2E = I N S U R E P R O P E R V E N T I L A T I O N B Y M A I N T A I N I N G 4" (102m m ) (M I N .) C L E A R A N C EF R O M C A B I N E T L O U V E R S T O W A L L .A S EG U R E U N A V E N T I L A C I ÓN A D E C U A D A M A N T E N I E N D O U N E S P A C I O E 4" (102m m ) (M ÍN .) D EH O L G U R A E N T R E L A R E JI L L A D E V E N T I L A C I ÓN D E L M U E B L E Y L A P A R E D A S S U R E Z -V O U S U N E B O N N E V E N T I L A T I O N E N G A R D A N T 4" (102m m ) (M I N .) E N T R E L E S ÉV E N T S D E L E N C E I N T E E T L E M U R .F = P O W E R C O R D 4' (1219m m ) L O N G C A B L E E L ÉC T R I C O D E 4' (1219m m ) P I E , D E L A R G O C O R D O N D A L I M E N T A T I O N 4' (1219m m )G = W A L L S C R E W H O L E S A G UJ E R O S D E T O R N I L L O S D E P A R E D T R O U S D E V I S D U M U R H = 2 X 4 B L O CK I N G BL O Q U E O D E 2 X 4B L O C 2 X 4F I N I S H E D F L O O R P I S O A C A B A D O P L A N C H E R F I N IL E G E N D /L E Y E N D A /L ÉG E N D E A = R E C O M M E N D E D W A T E R S U P P L Y L O C A T I O N 3/8 O .D . U N P L A T E D C O P P E R T U B E C O N N E C T S T U B O U T 1-1/2 I N . (38m m )F R O M W A L L S H U T O F F B Y O T H E R S S E R E C O M I E N D A U B I C A R E L T U B O C O R T O D E C O N E X I ÓN A L T U B O D E C O B R E S I N C H A P A R D E 3/8" D E D I ÁM . E X T . A 1-1/2"(38 m m ) F U E R A D E L A L L A V E D E P A S O E N L A P A R E D C O L O C A D A P O R T E R C E R O S . E M P L A C E M E N T R E C O M M A N D É D 'A L I M E N T A T I O N E N E A U P A R T U B E E N C U I V R E N O N P L A Q U É D E 3/8 P O . (9,5 m m ) D .E .C O N N E C T A N T U N E T U Y A U T E R I E D E 1-1/2 P O . (38 m m ) D E P U I S L E R O B I N E T D 'A R R ÊT F O U R N I P A R D 'A U T R E S .B = R E C O M M E N D E D L O C A T I O N F O R W A S T E O U T L E T 1-1/4 O .D . D R A I N U B I C A C I ÓN R E C O M E N D A D A P A R A E L D R E N A J E D E S A L I D A D E A G U A , D E 1¼ D E D I ÁM E T R O .E M P L A C E M E N T R E C O M M A N D É P O U R L E D R A I N D E D .E . 1-1/4" D E S O R T I E D E A U .C = 1-1/4 T R A P N O T F U R N I S H E D P U R G A D O R D E 1¼ N O P R O P O R C I O N A D O S I P H O N 1-1/4 N O N F O U R N I D = E L E C T R I C A L O U T L E T L O C A T I O N U B I C A C I ÓN D E L A T O M A D E E L E C T R I C I D A D E M P L A C E M E N T D E L A P R I S E D E C O U R A N T97321C (7/98)PUSH BUTTON VALVE ADJUSTMENTFIG. 3ADJUST THIS SCREW TO ELIMINATE VALVE LEVER "FREE PLAY" OR CONTINUOUS FLOW FROM BUBBLERSTREAM HEIGHTADJUSTMENT SCREWFIG. 422389101,20,24CORRECT STREAM HEIGHTFIG. 597321C (7/98)ITEM NO.PART NO.DESCRIPTION15005C 51544C 10-15075-31-55010-14534-31-64010-26399-31-64016-02705-08-64017-14037-42-59026860C 26861C 26862C 31513C 35762C 31027C 35766C 19-42439-01-55019-26684-51-55045688C 66229C 40136C 50986C 60-14181-51-55066506C 55880C 61314C 66202C 75494C 55996C 55913C 55885C 15008C 70682C See Color Table See Color Table See Color TableNut-Regulator Retaining BubblerPush Button Stem Cap Push Button Drain Plug Strainer Plate BasinRegulator Lever Pivot BracketRegulator Retaining Bracket Cold ControlCompressor Service Pak Overload/Relay Assy Relay Cover Electrical Shield Power Cord PrecoolerHeat ExchangerW ater Temperature Valve Regulator Holder Condenser Assy EvaporatorRegulator Mounting Bracket Regulator DrierCheck Valve StrainerAdaptor-Drain W/O Holes Nut 1-1/4 Slip Joint Nipple - Bubbler Tee - 1/4Side Panel - Right Side Panel - Left Front PanelPlatinum (PV)Almond (AV)Slate (SV)Stnlss Stl (SS)40153624841026912C 40153624844040153624283040153634841026908C 40153634844040153634283040150744841026904C 4015074484404015074428302222 CAMDEN COURT OAK BROOK, IL 60523PRINTED IN U.S.A.RIGHT PANEL FRONT PANEL COLOR LEFT PANEL *INCLUDES RELAY & OVERLOAD. IF UNDER WARRANTY , REPLACE WITH SAME COMPRESSOR USED IN ORIGINAL ASSEMBLY .NOTE: All correspondence pertaining to any of the above water coolers or orders for repair parts MUST include Model No. and Serial No. of cooler,name and part number of replacement part.ITEMIZED PARTS LIST123456789101112*131415161718192021222324252627282930313233NSFIG. 6CONDENSER WATER VALVE ADJUSTMENTThe condenser water valve is f actory preset f or a condenser water outlet temperature of 95° to 105° F.If actual temperature varies greatly f rom this, readjust water f low rate at the valve using the f ollowing procedures.1.START UP COMPRESSORThis can be accomplished by depressing the cooler push button (See Fig. 1 - Item 4). Keep water running during the entire readjustment procedure.2. ADJUSTMENT CONDENSER WATER VALVEAdjust valve by rotating adjustment stem. Rotating stem clockwise will decrease water flow. Counterclockwise rotation will increase water f low. Increasing water f low will result in a lower condenser outlet temperature, while decreasing water flow will result in a higher outlet temperature. Proper adjustment is attained when condenser outlet temperature is 95° to 105° F .WIRING DIAGRAMThis drawing is merely for illustrating the components of the electrical system.。

化工进展Chemical Industry and Engineering Progress2024 年第 43 卷第 2 期气力输送颗粒系统中静电的研究进展刘浩宇1，赵彦琳1，姚军1，WANG Chi-Hwa 2（1 中国石油大学(北京)机械与储运工程学院，清洁能源科学与技术国际联合实验室，过程流体过滤与分离技术北京市重点实验室，北京 102249；2 新加坡国立大学化学与生物分子工程系，新加坡 肯特岗 117585）摘要：在过去的几十年里，由于许多工业问题和相关新技术的发展，颗粒和颗粒流的静电学得到了越来越多的关注。

颗粒-颗粒和颗粒-壁面之间发生碰撞从而产生静电。

静电的发生会受多种因素的影响，随着颗粒与壁面之间的接触会在它们的表面产生静电荷的积累，静电量可以达到饱和状态。

本文分别综述了气力输送颗粒系统中的静电发生及静电平衡，着重分析了颗粒与壁面之间接触带电的两种方式（碰撞带电和摩擦带电）、颗粒流模式及受力情况，讨论了颗粒带电过程所受的影响因素，包括外界条件（温度、相对湿度）、颗粒几何条件（尺寸、形状、接触面积、粗糙度）以及受力条件（摩擦力、常压）等。

此外，对气力输送颗粒系统中静电的数值计算作了简单介绍。

最后，为澄清气力输送颗粒系统中静电发生的机理，对单颗粒发生静电的物理机制进行了分析。

根据对相关研究结果的总结，发现由于碰撞或摩擦造成的电荷转移的工作机制尚未完全明了，这些问题将在未来逐步得到解决。

关键词：静电效应；颗粒；气力输送；接触带电中图分类号：TH3；TQ012 文献标志码：A 文章编号：1000-6613（2024）02-0565-14Research advances of electrostatics in pneumatic conveyinggranules systemsLIU Haoyu 1，ZHAO Yanlin 1，YAO Jun 1，WANG Chi-Hwa 2(1 International Joint Laboratory on Clean Energy Science and Technology, Beijing Key Laboratory of Process FluidFiltration and Separation, College of Mechanical and Transportation Engineering, China University of Petroleum-Beijing, Beijing 102249, China; 2 Department of Chemical and Biomolecular Engineering, National University of Singapore,Kent Ridge 117585, Singapore)Abstract: In past decades, the electrostatics of granules and granular flows has obtained more and moreattention due to many industrial problems and development of new technologies. The collisions between granule-granule and granule-wall generate electrostatics. The occurrence of electrostatic can be affected by a variety of factors. As the contact between the granular and the wall, the accumulation of electrostatic charge on their surfaces can reach to an equilibrium state. The present work reviewed electrostatic generation and electrostatic equilibrium in pneumatic conveying granules systems. Two main contact charging ways between granule and wall (collision electrification and friction electrification), granular flowpattern and dynamic analysis were analyzed emphatically. The factors affecting the charging process of综述与专论DOI ：10.16085/j.issn.1000-6613.2023-1341收稿日期：2023-08-07；修改稿日期：2023-09-14。

Optik124 (2013) 2115–2120Contents lists available at SciVerse ScienceDirectOptikj o u r n a l h o m e p a g e:w w w.e l s e v i e r.d e/i j l eoFocal length and radius of curvature measurement using coherent gradient sensing and Fourier fringe analysisJitendra Dhanotia,Shashi Prakash∗Photonics Laboratory,Department of Electronics&Instrumentation Engineering,Institute of Engineering&Technology,Devi Ahilya University,Khandwa Road,Indore452017,Indiaa r t i c l e i n f oArticle history:Received26January2012 Accepted18June2012Keywords:Focal lengthFourier transformCollimationCoherent gradient sensing a b s t r a c tA procedure for the measurement of focal length and radius of curvature of a lens using coherent gradient sensing system and Fourier transform fringe analysis technique has been demonstrated.Light from the laser illuminates the specimen and the wavefront emerging from the specimen is tested using coherent gradient sensing interferometer.The fringe pattern corresponding to the test wavefront is stored,and analyzed using Fourier fringe analysis technique.The slope of the wavefront in the direction of shear has been evaluated.It provides the information regarding exact location of points corresponding to the focus/center of curvature of the lens.High accuracy and precision has been achieved.© 2012 Elsevier GmbH. All rights reserved.1.IntroductionCoherent Gradient Sensing(CGS)is double grating lateral shearing interferometric technique used extensively in various engineering applications.The technique has been operated in two primary domains,transmission and reflection.Based on these domains,the technique has been employed in thefield of exper-imental mechanics for slope and curvature measurement[1],crack tip deformation study[2,3]stressfield examination[4],etc.The technique has also been used for the measurement of residual stress in thinfilms[5].Focal length is an important optical parameter which needs to be known precisely in various optical systems.Initially clas-sical methods based on geometrical optics were used such as nodal slide,image magnification,focometer,etc.,but in recent times automated measurement using interferometric techniques has been preferably used.Various modern techniques reported for the measurement of focal length/radius of curvature are based on phenomenon of interference,diffraction,etc.Some of the tech-niques reported in this category are based on Talbot effect[6–8], Lau effect[9],digital moiréeffect[10],etc.Nakano and Murata[6]described a method based on Talbot interferometry for the measurement of focal length.They mea-sured the focal length in two ways:by measuring inclination angle of moiréfringes and by measuring the spacing between the moiréfringes.Bhattacharya and Aggarwal[7]determined the focal length∗Corresponding author.Tel.:+917312361116x7/9977186156;fax:+917312764385.E-mail address:sprakash davv@(S.Prakash).of a collimated lens using Talbot effect and moirétechniques.The defocusing of collimating lens is measured as a function of incli-nation angle of the moiréfringes.Sriram et al.[8]used dualfield grating system in Talbot interferometry for the measurement of focal length of a positive lens by placing the test lens in between the two gratings.The direct measurement of focal length of the test lens was undertaken by measuring separation between‘f’and ‘2f’planes corresponding to the test lens.The ease of detecting the exact location of these two planes has been improved based on principles of Talbot interferometry.Lei and Dang[11]reported the method based on grating shearing interferometry for the measurement of focal length of a lens.The lateral shift between the undiffracted zero order and diffractedfirst order has been mea-sured and used for the determination of focal length.Prakash et al.[9]reported the Lau based technique using incoherent light source to improve the accuracy of focal length measurement.Horner [12]used a simple method based on the observation of Fourier transform intensity pattern of a rectangular slit placed in front of the test lens.The focal length is measured in terms of separation between the zeros of the Fourier transform intensity pattern. The measurement is independent of the degree of collimation of incident beam or the principal plane of the test lens.Matsuda et al.[13]used the multiple beam shearing interferometry for the mea-surement of focal length.Xiang[14]developed retrocollimation interferometry based measurement in which focal length has been determined using Newton’s displacement ter,simple technique using diffraction characteristics of a circular Dammann grating has been used to locate the focal point of a lens[15].Lawall [16]used the spectroscopic approach in Fabry–Perot interferom-eter for the determination of radius of curvature of a concave mirror.Recently,Abdelsalam et al.[17]used the multiple beam0030-4026/$–see front matter© 2012 Elsevier GmbH. All rights reserved. /10.1016/j.ijleo.2012.06.0532116J.Dhanotia,S.Prakash/Optik124 (2013) 2115–2120Fig.1.Basic principle of coherent gradient sensing system. interference phenomenon in reflection mode for the measurement of radius of curvature of spherical smooth surfaces.In the above-mentioned techniques the measurement is based on the visual inspection alone;the results obtained are not quan-titative and are subject to vary based on the visual perception of human senses.Also,the measurement characteristics of the tech-niques were relatively poor.As an alternative to these techniques, direct phase measuring techniques,such as phase shifting method and Fourier transform method have been reported.These have tremendously improved the measurement characteristics in terms of accuracy,precision,and sensitivity achievable.Singh et al.[18] combined four-step phase shifting technique with Fourierfiltering method and correlated the slope of the phase map with the focal length of the test lens.Tay et al.[19]reported focal length mea-surement using phase shifted Lau phase interferometry.However, phase shifting test procedure requires specialized hardware(pre-cision controlled translation stage and associated equipment)and recording of several interferograms to determine the phase.This makes the technique tedious and relatively cumbersome.Toward achieving automation and better measurement char-acteristics,the Fourier Transform Method(FTM)has been used extensively in various scientific and engineering applications. Takeda et al.[20]used the Fourier transform method of computer based fringe pattern analysis for topography and interferometry. The method has been used to make clear distinction between ele-vation and depression of the object,even from a single non-contour type of fringe pattern.The Fourier transform method has been used for applications such as the measurement of3D surface profile[21], temperature[22],distance[23],slope[24],etc.In our previous paper[25],the CGS technique has been employed for collimation testing of an optical beam.In present communication,we report our investigation undertaken toward measurement of focal length and the radius of curvature by using CGS technique.The wavefront emerging from the optical element under test is passed through the CGS interferometer.The exact location of the focal point/center of curvature is determined by analyzing the shearing interferometric fringes generated in the CGS interferometer.Direct wavefront phase based data has been retrieved from the shearing interferometric fringes,using Fourier fringe analysis technique.The information regarding the slope of wavefront phase provides improved accuracy and precision in locating the exact focal point/radius of curvature.2.TheoryThe basic principle of coherent gradient sensing based inter-ferometer is shown in Fig.1.The expanded and collimated laser beam is incident on a pair of Ronchi gratings G1and G2having the same pitch‘p’and an arbitrary separation‘d’.Beyond the grat-ing G1emerge several diffraction orders.For simplicity,only the zeroth and thefirst orders(±1)are considered to propagate inthe Fig.2.Schematic of the experimental arrangement for measurement of focal length of the test lens using coherent gradient sensing and FTM.forward direction.The magnitude of the angle between the propa-gation directions of the zeroth and thefirst order beams is given by the diffraction equationÂ=sin−1( /p),where is the wavelength of light and p is the grating period.These beams after being inci-dent on the second grating G2,are further diffracted into orders such as E(0,0),E(+1,0),E(0,+1)and so on.These wavefronts which propagate in different directions are brought to focus at spatially separate diffraction spots at the focal plane of the lens L1.Out of these,the spot corresponding to thefirst order(E+1,0,E0,+1)is seg-regated and allowed to propagate;rest are blocked using a spatial filter placed at the back focal plane of the lens.Under this condi-tion,the interferometer acts as a shearing interferometer,bearing fringes of sinusoidal profile in the common area between the two wavefronts.The basic schematic of experimental arrangement for the mea-surement of focal length is shown in Fig.2.Expanded and collimated light from the laser is made incident onto the test lens.Beyond the test lens is placed a mirror M.Light reflected from the mirror passes through the test lens.The wavefront emerging from the lens is diverted for the purpose of testing using the beam splitter.Testing is undertaken using CGS interferometer.CGS is basically a grat-ing shearing interferometer.Corresponding to orders(E+1,0,E0,+1) propagated beyond the gratings,the original wavefront and the sheared wavefront emerge.The shearing between the test and the sheared wavefront may be varied by varying the grating separation.Toward making suitable adjustments for undertaking the mea-surement of focal length,the mirror is moved along the optic axis with respect to the test lens.Corresponding to the different positions of the mirror,the‘defocus’error gets introduced in the wavefront,if the mirror is not at exact focus of the lens.An addi-tional error‘wavefront tilt’is introduced by tilting the grating by small angle with respect to each other.The wavefront is then inci-dent on the grating shearing interferometer for testing.The output of the grating shearing interferometer yields a particular type of fringe pattern depending upon the gradient of wavefront errors in the direction of shear[26].Hence,corresponding to the type of wavefront emerging from the test lens,the orientation of the fringes appearing at the output of the interferometer is different.When the separation between the test lens and the mirror is equal to the focal length of the test lens,the wavefront emerging from the test lens is plane.Under this condition the horizontal straight line fringe pattern is obtained.For in-focus and out-focus position,the wave-front emerging out is diverging and the converging,respectively. For the converging or the diverging wavefront the fringe orienta-tion gets inclined at a positive or the negative angle with respect to the horizontal.Fig.3(a)–(c)corresponds to the fringes obtained at in-focus,at-focus and out-of-focus position of the mirror with respect to the defocusing lens(test lens),respectively.To increase the measurement accuracy in the determination of focal point of the test lens,the Fourier fringe analysis of the interferograms isJ.Dhanotia,S.Prakash/Optik124 (2013) 2115–21202117Fig.3.Fringe patterns recorded using CCD camera(a)at in-focus position of the mirror with respect to test lens of focal length240mm,(b)at at-focus position of the mirror with respect to test lens of focal length240mm,and(c)at out-of-focusposition of the mirror with respect to test lens of focal length240mm.Fig.4.Flow chart for a Fourier transform algorithms. undertaken and direct phase˚(X,Y)of the wavefront determined. Fig.4shows the algorithm for undertaking Fourier fringe analysis. The theoretical treatment regarding the Fourier transform method has been explained in Ref.[20].The slope of the phase map pro-vides information about the type of the wavefront.The slope in case of at focus,out focus and in focus position is almost zero,pos-itive and negative respectively.The separation between the lens and the mirror is determined,to yield the focal length.Measurement of radius of curvature has also been undertaken. Fig.5shows the schematic of the experimental arrangement for the measurement of radius of curvature of the concave mirror.The measurement is based on the fact that the distance between two positions at which the incident collimated beam retraces its path after reflection from spherical test surface,is equal to its radius of curvature.The Fourier transform algorithm as mentioned above has been used for the interferogram analysis.3.Experimental detailsThe experimental setup for the measurement of focal length using coherent gradient sensing is shown in Fig.2.He–Ne laser of15mW( =632.8nm)was used as a light source.Light fromthe Fig.5.Schematic of the experimental arrangement for measurement of radius of curvature of the concave mirror using coherent gradient sensing and FTM.He–Ne Laser is spatiallyfiltered using a combination of pinhole of5␮m diameter and microscopic objective of magnification45×. The precision achromatic doublet lens PAC088supplied by New-port Corporation,USA,having a focal length of250mm,has been used as collimationg lens L C.In the path of collimated beam,the lens under test has been introduced.Beyond the lens is introduced a mirror M mounted on the precision translating stage(NF5DP20/M) supplied by Thorlabs Inc.,USA,to translate it along the optical axis. The reflected beam from the mirror M back-propagates through the lens.This beam is deflected using a beam splitter BS for detec-tion of the defocusing errors.Two gratings,G1and G2of period 0.08mm each,have been placed in tandem such that grating lines of two makes equal but opposite angle with respect to the ver-tical.The beam corresponding to thefirst order spot is isolated using a spatialfiltering arrangement comprising of the combina-tion of two lenses and an aperture A.Separation of various orders depends on the period of the gratings used.The shear fringes are formed due to superposition of laterally shiftedfirst order beams diffracted from gratings G1and G2.The shearing interferogram was imaged on the phase plate of CCD camera using lenses L1and L2. Aperture A is placed at the focal plane of the lens L1to allow the desired diffracted order to reach the image plane.The CCD is hav-ing1392×1040pixels with each pixel sized4.65␮m×4.65␮m. For image acquisition and display,CCD camera interfaced with the frame grabber card has been used and the results were displayed on-line onto the computer monitor.To experimentally determine the values of accuracy and pre-cision in the measurement of focal length,the plane mirror M (specimen)mounted on the translation stage is translated upscale and downscale,so that one approaches the focal position/radius of curvature in either direction.Initially,the mirror is placed nearer to the test lens.The mirror is then moved away(in+Z direction) from the test lens.As the mirror approaches the focal point of the test lens,the straight line fringes oriented at a positive angle with respect to the horizontal reference appear.This corresponds to the condition when the wavefront emerging from the lens is diverging.Fig.3(a)corresponds to the position when the wave-front is diverging.As the mirror is moved further the inclination angle of the fringes decreases and they rotate in the clockwise direction.The fringes slowly become parallel to the horizontal as the focal position is reached.Fig.3(b)corresponds to this position. For thefine setting of the focal position a series of interferograms were recorded near this position and analyzed using FFT algorithm. Fig.8(a)and(b)shows the phase plots(obtained using FFT analy-sis)of the recorded interferograms in case when the wavefronts are diverging and plane,respectively.As the mirror is further moved along the optic axis,in the direction same as above and the‘in-focus’position is approached,the wavefront emerging from the test lens becomes converging.The inclination angle of the fringes further decreases and rotates in the clockwise direction.At this position,2118J.Dhanotia,S.Prakash/Optik124 (2013) 2115–2120Fig.6.Fourier spectrum of recorded image for(a)in-focus position of the mirror with respect to test lens,(b)at-focus position of the mirror with respect to test lens, and(c)out-of-focus position of the mirror with respect to test lens.the inclined fringes appear at a negative angle with respect to the horizontal.Figs.3(c)and8(c)corresponds to fringe pattern and the phase plot,respectively.Experiments for the measurement of radius of curvature of reflective surface has also been undertaken.In the experimental set-up of Fig.2the plane mirror has been replaced by the con-vex/concave mirror.A typical set-up for the measurement of radius of curvature of concave mirror is shown in Fig.5.Collimated beam is incident on the corrected lens C L.Beyond the converging lens the beam converges and is incident onto the concave mirror under test.As per the test procedure,the concave mirror is translated along the optic axis till it reaches the focal plane of the corrected lens.At this position,the horizontal fringe pattern is obtained at the image plane.Next,the concave mirror is translated along the optic axis(away from the corrected lens)till the horizontal fringe pattern is again obtained.Now,the series of interferograms were recorded near this position and the exact location of the center of curvature determined using the Fourier transform method.The minimum value of the slope of the phase map has been used as the criterion for the exact determination of the center of curvature of the reflecting surface.The difference between the two positions of the concave mirror,F L and D LM,as shown in Fig.5,may be treated as the correct value of radius of curvature.The similar procedure may be repeated for the convex mirror also.4.Results and discussionExperimental results verify that the measurement of focal length using coherent gradient sensing can be performed advan-tageously.For each position of the mirror the interference patterns are recorded and the images were stored in the Computer mem-ory.For the detection of exact focal length of the test lens,a series of interferogram were recorded near the focus position of the test lens.The measurements were undertaken at several positions of the test lens along the axis;however the results were presented for only three positions.Fig.4corresponds to the proposed Fourier transform algorithm used to extract the phase even from the single interferogram.The Fourier transform method involves taking FFT of the interferogram to obtain its Fourier spectra.Fig.6(a)–(c)shows the Fourier spec-tra of the recorded interferograms corresponding to Fig.3(a)–(c), respectively.In the Fourier spectra the central dot having the maxi-mum intensity shows the zero order while the dots immediately on the two sides of the central spot,show the±1order spectra.Next, thefirst order Fourier spectra was selected and shifted to the cen-ter position.The inverse Fourier transform of the centrally shifted spectra provides the necessary phase information of the recorded interferogram.Fig.7(a)–(c)shows the plot of evaluated phase map with respect to the pixel position for‘in-focus’,‘at-focus’and‘out-of-focus’position of the mirror with respect to the test lens.To obtain reliable phase map,thefield corresponding to the wrapped phase map has been scanned and2 is added or subtractedevery Fig.7.Unwrapped Phase map for a fringe pattern corresponding to(a)in-focus position of the mirror with respect to test lens of focal length240mm,(b)at-focus position of the mirror with respect to test lens of focal length240mm,and(c)out-of-focus position of the mirror with respect to test lens of focal length240mm.time an edge is detected.The phase values so obtained are plotted against the pixel values using MATLAB toolbox.Fig.8(a)–(c)shows the two-dimensional plot of the evaluated phase map with respect to the pixel position for‘in-focus’,‘at-focus’and‘out-of-focus’posi-tion of the mirror with respect to test lens.From the results,it is quite evident that the slope of the phase map is positive for the‘in-focus’position of the mirror with respect to test lens.Plot of phase˚with respect to x domain for afixed value of y,gives a positive slope as anticipated and shown in Fig.8(a). The slope of the phase map decreases as we move toward‘at-focus’position and it approaches zero at the‘at-focus’position of the test lens.This corresponds to the exact focal position of the test lens. The plot of phase˚with respect to x domain,for thefixed value of y(plot of˚along the same row for different values of column vector)gives a straight line as anticipated and is shown in Fig.8(b). As the mirror is moved away from focal position of test lens,the slope of phase maps becomes negative.Negative slope indicates the out-focus’position of the mirror with respect to test lens.Plot of phase˚with respect to x domain for afixed value of y,hasaFig.8.Variation of phase with respect to x-axis for the fringe pattern corresponding to(a)in-focus position of the mirror with respect to test lens of focal length240mm;(b)at-focus position of the mirror with respect to test lens of focal length240mm; and(c)out-of-focus position of the mirror with respect to test lens of focal length 240mm.J.Dhanotia,S.Prakash/Optik124 (2013) 2115–21202119Table1Comparison of the measured values of focal lengths with the standard values of focal lengths.Also,variation of f with the focal length f for grating separation of28mm. S.No.f(mm)Measured f(mm) f(mm)( f/f)×1001150149 1.00.66660.886 2180178.5 1.50.83330.65574 3220217.7 2.3 1.0454 1.75214 4240237 3.0 1.25 2.04817 5290286.2 3.8 1.3103 1.58902negative slope as shown in Fig.8(c).Hence,the focal point of the test lens can be determined very precisely and accurately.The distance between the focal point and the test lens is a direct measure of the focal length.The discussion regarding the comparison of accuracy or rela-tive error in the present case with previous reported literature also needs consideration.The accuracy obtainable in the focal length measurement may be defined as the smallest detectable devia-tion from the perfect focal position,‘ f’of the test lens.This value ‘ f’depends on the focal length,‘f’of the test lens.The percent-age accuracy of the focal length measurement technique has been defined as‘( f/f)×100’.The comparison of the accuracy defined as above,for different techniques reported till date looks most pertinent.Nakano and Murata[6]measured the focal length of 400cm lens with an accuracy of2%corresponding to±1◦accu-racy in inclination angle measurement.Bhattacharya and Aggarwal measured the focal length of the collimating lens as a function of inclination angle of the moiréfringes and achieved an accuracy of 2%of true value.Lei and Dang[11]used the plano-convex lens of focal length77mm and cylindrical plano-convex lens of focal length116mm and obtained an accuracy of1.4%.Keren et al.[27] reported0.8%accuracy using the fringe counting approach for a lens of25mm focal length.Prakash et al.[9]demonstrated the measure-ment of focal length for the lenses of different focal lengths using Lau interferometric arrangement and reported an accuracy of0.7%. Singh et al.[18]reported an automated method for the focal length measurement using temporal phase shifting technique in Talbot interferometry.The authors reported the relative comparison of the accuracy achievable in various focal length measuring test pro-cedures.They correlated the focal length of a test lens with the obtained phase map and reported an accuracy of0.246%for the lens having focal length of240mm.Tay et al.[19]reported an accuracy of0.2%in focal length measurement of a50mm convex lens,using three-step phase shifting algorithm in Lau phase interferometry.The results of the measurement undertaken with the lenses of different focal lengths are shown in parison of the results obtained with those using above-mentioned techniques reveal that,we could measure the focal length more accurately using the proposed technique.To check for the precision of tech-nique,standard deviation( )has also been calculated in each case. The smaller values of standard deviation reveals that the focal point position(hence the focal length)can be determined precisely using this method.The technique has also been used to test the concave mirror of radius of curvature200mm.The relative error r/r for the measurement of radius of curvature was determined to be0.25%. Hence,the measured radius of curvature of the concave mirror shows the close agreement with the standard.The discussions regarding the error in the present system also need consideration.The errors may occur in the system due to mis-alignment of the gratings,quality of optics used,imperfections in the gratings,improper collimation of optical beam,aberrations in lens,etc.Care has been taken to minimize these errors.The pre-cision translating device may also be the cause of systematic or human error.Random error may also affect the accuracy of the sys-tem.Random errors are those remaining when all systematic and gross errors have been taken care of.These are attributed tovarious parameters that affect the system in random fashion.We have taken precautions to minimize these errors.There may be errors due to quantization errors in digitizing the data,source instabilities, and detector non-linearity.Since,it is an interferometric technique the influences of environmental factors such as extraneous vibra-tions and air turbulence have to be taken care of.5.ConclusionsThe accurate measurement of focal length and radius of cur-vature using coherent gradient sensing technique coupled with Fourier transform method has been successfully demonstrated.To check for the validity of the technique,the results of the experimen-tal investigation have been compared with the other techniques. There are some major advantages in this method.(i)The method is simple and direct.The components used areinexpensive.(ii)Method is well adoptable to be used in industrial environment because it is a common path interferometer.The automated interferogram analysis using Fourier fringe analysis involves use of single interferogram,and hence the effect of shock and vibration in measurement may be minimized.(iii)Relative to the self-imaging methods devised earlier,the errors due to in accurate grating seperation may be completely elim-inated.(iv)The profile of recorded fringe pattern in CGS is sinusoidal and devoid of grating noise as in case of Talbot/Lau based interfer-ometers.Hence,higher accuracy and precision of measurement as com-pared to other similar techniques has been reported. AcknowledgementThefinancial support of University Grants commission(UGC), New Delhi in terms of research project grants33-395/2007(SR)is gratefully acknowledged.References[1]H.V.Tippur,Simultaneous and real-time measurement of slope and curvaturefringes in thin structures using shearing interferometry,Opt.Eng.43(2004) 1–7.[2]H.V.Tippur,S.Krishnaswamy,A.J.Rosakis,A coherent gradient sensor for cracktip deformation measurements:analysis and experimental results,Int.J.Fract.48(1991)193–204.[3]H.V.Tippur,S.Krishnaswamy,A.J.Rosakis,Optical mapping of crack tip defor-mations using the methods of transmission and reflection coherent gradient sensing:a study of crack tip K,dominance,Int.J.Fract.52(1991)91–117. [4]L.Xu,H.V.Tippur,C.E.Rousseau,Measurement of contact stresses using realtime shearing interferometry,Opt.Eng.38(1999)1932–1937.[5]T.S.Park,S.Suresh,A.J.Rosakis,J.Ryu,Measurement of full-field curvature andgeometrical instability of thinfilm-substrate systems through CGS interferom-etry,J.Mech.Phys.Solids51(2003)2191–2211.[6]Y.Nakano,K.Murata,Talbot interferometry for measuring the focal length ofa lens,Appl.Opt.24(1985)3162–3166.[7]J.C.Bhattacharya,A.K.Aggarwal,Measurement of the focal length of a collimat-ing lens using the Talbot effect and the moirétechnique,Appl.Opt.30(1991) 4479–4480.[8]K.V.Sriram,M.P.Kothiyal,R.S.Sirohi,Direct determination of focal length byusing Talot interferometry,Appl.Opt.31(1992)5984–5988.[9]S.Prakash,S.Singh,A.Verma,A low cost technique for automated measurementof focal length using Lau effect combined with moiréreadout,J.Mod.Opt.53 (2006)2033–2042.[10]S.D.Nicola,P.Ferraro,A.Finizio,G.Pierattini,Reflective grating interferometerfor measuring the focal length of a lens by digital moiréeffect,mun.132(1996)432–436.[11]F.Lei,L.K.Dang,Measuring the focal length of optical systems by grating shear-ing interferometry,Appl.Opt.28(1994)6603–6608.[12]J.L.Horner,Collimation invariant technique for measuring the focal length of alens,Appl.Opt.28(1989)1047–1048.。

Precision Engineering 45(2016)203–208Contents lists available at ScienceDirectPrecisionEngineeringj o u r n a l h o m e p a g e :w w w.e l s e v i e r.c o m /l o c a t e /p r e c i s i onEffects of molding conditions on injection molded direct joining using a metal with nano-structured surfaceFuminobu Kimura ∗,Shotaro Kadoya,Yusuke KajiharaInstitute of Industrial Science,The University of Tokyo,4-6-1Komaba,Meguro-ku,Tokyo 153-8505,Japana r t i c l ei n f oArticle history:Received 14December 2015Received in revised form 5February 2016Accepted 16February 2016Available online 3March 2016Keywords:Metal-plastic direct joining Injection molding Nano-structuresTensile shear strengtha b s t r a c tInjection molded direct joining (IMDJ)is one of the metal-plastic direct joining processes and is based on a combination of a special surface treatment of a metal piece and an insert molding.This study employed a chemical processing as the special surface treatment to form nano-structures on the metal piece.We investigated relationship between joining strengths and molding conditions;we focused on pressure of a mold cavity and injection speed as molding conditions in this work.To evaluate the IMDJ samples processed under various molding conditions,we carried out tensile-shear tests.Then we compared the results of the tests to discuss how much each condition variation affected the joining strength.From the discussion,we found an interesting effect of the injection speed,which is unique to the IMDJ using a metal piece with nano-structures.The findings of this study will promote a better understanding of the IMDJ.©2016Elsevier Inc.All rights reserved.1.IntroductionJoining metal and plastic structures is one of the impera-tive techniques for modern manufacturing fields.These dissimilar material structures are usually joined by using adhesives or mechanical joint such as bolt screws and rivets [1,2].Meanwhile,a novel technique that directly joins metal and plastic structures without such extra parts has attracted attentions recently [3].The direct joining technique has many advantages against the typical joining;for example it can reduce weight,can simplify manufactur-ing processes,and can ease designing restrictions.Some research groups,therefore,have tried to realize the direct joining by using various means.The joining means are roughly categorized into two groups by methods forming plastic structures.One is that the plastic struc-ture is formed previously and then the plastic and metal structures are joined (a separated type).The other is that the forming plas-tic structure and joining are processed simultaneously (an in-situ type).For the separated type,a plastic base and a metal base are put to contact each other and are joined by various types of local heating;for example,a laser-induced local heating [4–8],a friction spot joining [9],a friction lap welding [10],and an ultrasonic weld-ing [11].The local heating melts the plastic base or the metal base at contacted area;and then the bases are joined after cooling and∗Corresponding author.Tel.:+81354526466.E-mail address:fuminobu@iis.u-tokyo.ac.jp (F.Kimura).hardening.This type,however,has some limitations about materi-als or shape/size of the joint structures since thermal energy caused by the local heating must reach on the interface.The in-situ type that forms a plastic structure and joins it to a metal base simultaneously utilizes an injection molding with inserting a special metal piece.In this study this type method is called an injection molded direct joining (IMDJ).To join the plas-tic to the metal in a mold,a special treatment is processed on a surface of the metal piece.The proposed surface treatments have been various types;e.g.chemical coupling layer coating [12–14]or micro/nano-structure forming [15–21].Regarding the chemical coupling layer coating,a surface of a molded plastic is chemically bound with the metal via the coated layer.This type,however,has material limitation caused by affinities between the layer and the materials.By contrast,the micro/nano-structure forming type is based mainly on mechanical interlocking between the surface structures and the molded plastic.The proposed forming methods use abrasive blasting [15,16],laser processing [17–19]and chemi-cal processing [20,21].In comparison with chemical coupling layer coating type,the micro/nano-structure forming type has few limi-tations since the base materials are joined structurally.The IMDJ using micro/nano-structure forming has not been well applied to real industries because of some remaining chal-lenges;nevertheless the IMDJ is a quite promising process.The challenges for industrial applications are as follows:(i)Actual join-ing mechanism has not been revealed.(ii)Relationships between processing conditions and product characteristics have not been investigated enough.(iii)The processing conditions have not been/10.1016/j.precisioneng.2016.02.0130141-6359/©2016Elsevier Inc.All rights reserved.204 F.Kimura et al./Precision Engineering45(2016)203–208Fig.1.Process overview of the injection molded direct joining.The process is com-posed of two key production processes;(a)surface treatment and(b)insert injection molding.optimized.Possible approaches to solve the challenges are to reiter-ate mechanical tests,analyses,and observations of boundaries for each joining sample processed under various conditions.Some pre-vious studies[15–18,20]have investigated effects of the processing conditions.However the investigations have been rarely conducted in the case that size of surface structures of the metal piece is nanometer scale.This study investigated the effects of molding conditions on strength of the IMDJ samples,of which metal pieces had surface nano-structures.Although there are many controllable molding conditions,target conditions of this work were mold cavity pres-sure and injection speed.We formed the nano-structures on the metal piece by a chemical processing.Then we produced IMDJ sam-ples,of which shape is a single lap joint geometry,to measure shear strength of joining by a tensile shear test.From measured strength, we discussed effects of molding conditions.2.Experimental procedure2.1.Joining processFig.1shows an overview of the production process.The IMDJ process is composed of two key processes:(a)a surface treatment of a metal piece and(b)an insert injection molding using the surface-treated metal bination of these processes enables the direct joining of metal and plastic structures.Details of each process and processing conditions used in this work are described in the following.2.1.1.Surface treatmentSome means of surface treatments have been proposed for the IMDJ[15–21].Since it is difficult to form the surface struc-tures in nanometer scale by using abrasive blasting[15,16]or laser processing[17–19],we utilized a chemical processing.We applied one of the chemical processing(Nano Molding Technology,Tai-seiplas[21])to the forming of nano-structures on surfaces of A5052 aluminum alloy pieces for the joining experiments.Fig.2shows an image of a surface of the treated metal(30◦tilted view)taken by a scanning electron microscope(SEM).From the SEM image,we can see a porous structure with pore diameters of approximately20nm.The structure consisted of not a simple array of(vertical)holes but a three-dimensionally foam network such as a sponge foam.The aluminum alloy pieces were treated under the same condition for whole joining experiments sincewe Fig.2.SEM image of a surface treated metal piece(30◦tilt).Porous structures were formed on the metal surface.The size of each pore was approximately20nm.focused on only the effects of molding conditions but not on the effects of surface structures in this study.2.1.2.MoldingIn this study,we utilized a commercial injection molding machine(ROBOSHOT˛-100iA Linear,FANUC)and an original mold. Fig.3shows a shape of the mold(cavity)for a single-lap joint sam-ple.The size of the main cavity(plastic body)and of the metal insert were10mm×50mm×3mm and18mm×l metal×1.5mm (width×length×thickness),respectively.The length of the metal insert,l metal,is selectable from two sizes:45mm(short type)or 50mm(long type).Along with the selection,length of overlap between the plastic body and the metal piece was changed as 5mm or10mm,and thus the joint area was5mm×10mm or 10mm×10mm,respectively.However strength of the IMDJ sam-ple processed by the long type mold was too large to be evaluated because of too large joint area,which is twice as large as the short type.We,then,used only the short type for the evaluation and analyses.The detail of the evaluation problem is given in Section3.1.A unique point of this mold is that a pressure sensor(6158A, Kistler Japan)and a temperature sensor(EPSSZT-04.0×030,Futaba Corporation)were installed to monitor cavity states.To estimate the pressure on the boundary surface,the pressure sensor was located near the joint area as shown in Fig.3.This is because the pressure on the boundary surface would be one of the most effective factors for plastic replication to the nano-structures and resultant joining strength.The melted plastic wouldflow into the nano-structures more easily under higher pressure on the bound-ary surface.By monitoring the cavity states with the sensors,we controlled the molding conditions.Process states of one cycle of the injection molding are as fol-lows[22];(I)queueing,(II)packing,(III)holding,(IV)cooling,and (V)ejecting.We can know the state during the molding by the cavity monitoring(especially monitoring pressure behavior).Fig.4 shows an example of time-course measurements of cavity pressure (upper)and temperature(lower).Pressure variations represent the molding states I to IV as shown in Fig.4.At the packing state(state II),the pressure rises rapidly,reaches a peak point,and sinks down rapidly as well.Then the cavity state changes to the holding state (state III),where the pressure keeps approximately steady value. Finally,the pressure decreases gradually since the plastic cools and hardens at the cooling state(state IV).The peak value at the state II and the steady value at the state III of the pressure are pack pres-sure,P p,and holding pressure,P h,respectively(Fig.4).These two types of the pressure values are the investigation objects of this study.Methods of controlling the pressure values are given in the following paragraphs.Table1shows molding conditions.Among them,this study focused on the pack pressure,P p,the holding pressure,P h,and theF.Kimura et al./Precision Engineering45(2016)203–208205Fig.3.Top and front-view of the mold used for the IMDJ process and isometric-view of a sample.A pressure sensor and a temperature sensor were installed on the mold tomonitor states.A surface treated metal piece is inserted into the insert cavity and a melted plasticflows in the maincavity.Fig.4.Example of cavity pressure and temperature monitoring.From the pressure behavior,we can see the state of injection molding.The peek pressure in the state II and the steady pressure in the state III are pack pressure,P p,and holding pressure, P h,respectively.injection speed,v.We investigated how the variations of these three condition parameters affected on the joining strength.Although most of the condition parameters can be adjusted on the injection molding machine,the pack pressure cannot be controlled directly. The molding machine can control injection force/pressure on a injection screw(an actuator of an injection unit).The injection force is,however,not always proportional to the cavity pressure because of viscosity of the melted plastic material.Therefore,dynamic cav-ity pressure,which is the varying pressure at state II,cannot be controlled without any feedbacks.On the other hand,(quasi-)staticTable1Molding conditions.Pack pressure P p MPa Injection speed v mm/s Holding pressure P h MPa Diameter of cylinder20mm Holding time length8s Temperature of mold140◦C Temperature of cylinder270/275/265/245/10/75◦C pressure,which is the pressure at state III,is controllable since it is not affected by the viscosity.The pack pressure(dynamic cavity pressure)was controlled to be approximately equal to a desired value by monitoring cavity state and giving the feedbacks of the monitored data manually. Based on the monitored pressure,we adjusted an amount of injec-tion volume,which could affect the pack pressure:if the injection volume is larger than a proper value,the pack pressure becomes higher,and vice versa.We used two groups of parameter combinations,G1and G2, as shown in Table2.For G1,the injection speed wasfixed as: v=300mm/s,and the pack pressure and the holding pressure was varied as:P p=60,90,and120MPa,P h=20,40,and60MPa.Thus, there were totally nine combinations of the molding conditions (=3×3).On the other hand,the both pressure conditions werefixed in G2as:P p=60MPa and P h=40MPa,but the injections speed was varied as:v=150,300,and600mm/s.These condition values were in the suitable ranges for practical use of the employed injection molding machine and mold.Note that the number of the IMDJ sam-ples for G1and G2are seven and ten,respectively(G1:n=7.G2: n=10).As a plastic material for the molding experiments,we utilized polybutylene terephthalate(PBT:Toraycon®1101G-X54,Toray) that contains glassfibers of30wt%.According to[16],thefiber-reinforced plastic is suitable for the IMDJ.We,therefore,selected this grade of PBT materials.The pelletized raw PBT materials wereTable2Values of varied condition parameters.The combinations of the parameters were divided into two groups,G1and G2.P p MPa P h MPa v mm/s2060403006020G1*******6020120403006040150G2*******40600206F.Kimura et al./Precision Engineering 45(2016)203–208Fig.5.Grippers of tensile test machine with the IMDJ sample.The sample was gripped with spacers to align the center of the grippers and the boundary surface of the sample.desiccated under an environment of 130◦Cfor over four hours before injection molding experiments.After the molding experiments,the samples were annealed for four hours at 130◦C to relieve residual stresses.Additionally,we removed extra parts of the sample such as a sprue and a runner parts to complete a single lap joint.2.2.Evaluation of joining strengthTo evaluate the IMDJ samples,we carried out tensile tests.The test measured tensile-shear strengths of the single lap joint sam-ples.Fig.5shows a photo image and a schematic illustration of the samples and grippers of a tensile test machine (AG-50kNG,SHI-MADZU).To apply shear load on the boundary of the single lap joint geometry,we aligned the center of the grippers on the boundary of the joining sample by gripping the sample with spacers.Lengths of both gripped ends and initial distance between grippers were 15mm and 60mm,respectively.The test machine applied strain to the sample with constant speed of 1mm/min.until the sample was broken.During the test,the test machine measured displace-ment of the grippers and load applied to the grippers.Fig.6shows an example of time-course measurements during the tensiletests.Fig.6.Example of time-course measurements of applied load and displacement by tensile test machine.The maximum load was recorded as the (shear)strength ofjoining.Fig.7.Photo image of the completed IMDJ sample molded by the short type mold (a)and the long type mold (b).By the tensile shear tests,the samples (a)were broken at boundary surface (a ),but some of the sample (b)were broken at the base material (b ).We recorded maximum load as the strength of the joining.Note that the samples were stored in a desiccator under an environment of approximately 24◦C and 40%RH for over twenty four hours before the tests.3.Results and discussion3.1.Measurement results and analysisInjection molded plastics were successfully joined to metal pieces under all molding conditions.Fig.7shows the completed IMDJ samples:(a)by the short type mold,(b)by the long type mold.There was no significant difference of appearance between the samples molded under each condition.Some problems,how-ever,occurred in pilot tensile tests.By some pilot tests for the samples processed by the long type mold,some base materials of the plastic parts were broken instead of the boundary surfaces of the joints (Fig.7(b )).In the case that the base material was bro-ken,we could not measure the correct strength of the joining.We,thus,used only the samples processed by the short type mold.All the samples processed by the short type mold were broken at the boundary surfaces (Fig.7(a )),and thus the correct strength could be measured.Fig.8shows measured strength for the sample processed under G1conditions group (varying pressure condition).In this figure,the holding pressure is the target value,which was set in the mold-ing machine.On the other hand,the pack pressure is the measured value,not the target value.The markers and the error bars are mean values and standard deviations,respectively.The plotted data in both graphs are in common but the different plotting manner.By outlier analyses,we excepted two outlier values in the two data sets obtained from (P p ,P h )=(60,60)and (90,40).Thus,in these two data sets,the numbers of samples were six (n =6).The numbers of samples of other data sets that have no outlier were seven (n =7).Although we used only three points of pressure ranges for each investigation,we could see tendencies that the strength slightly increased with the higher pressure conditions.Given that the pres-sure ranges were suitable for the practical use of the setups,we can say these investigations were enough to understand the effects of the pressures.Fig.9shows measured strength against injection speed (results for G2conditions).The markers and the error bars represent mean values and standard deviations,respectively.There was no outlierF.Kimura et al./Precision Engineering 45(2016)203–208207Fig.8.Measured strength against holding pressure,P h (a)and pack pressure,P p (b).The markers and the error bars represent mean values and standard deviations.The strength slightly increased with the higher cavitypressure.Fig.9.Measured strength against injections speed,v .The markers and the error bars represent mean values and standard deviations.The strength significantly decrease with the higher injection speed.in this case.For the injection speed,the strength decreased with the higher speed.The variation of the strength caused by the variation of the injection speed was much higher than by the cavity pressure variation.To analyze effects of each variable parameter,P h ,P p ,and v on the strength,we calculated coefficients of correlation,r ,in each case.The calculation was done by using following equation.r =(x i −x )(y i −y )(x i −x )2(y i −y )2(1)where y i is each value of the strength and x i is the value of each variable parameter corresponding to y i .The values x and y are aver-age values of x i and y i ,respectively.The calculated coefficients are shown in Table 3.From the coefficients,we can see that the holding and pack pressures had positive correlations (r :0.1–0.7).This is in agreement with the plots shown in Fig.8.On the other hand,the coefficient for the injection speed was negative,which is also valid with the plot shown in Fig.9.In comparison with the pressures,the injection speed had a significant correlation;the coefficients of the pressures were small positive (r :0.1–0.5),except P h in the case ofTable 3Calculated coefficients of correlation.Effect ofCaserP p =60,v =3000.358P hP p =90,v =3000.763P p =120,v =3000.267P h =20,v =3000.522P pP h =40,v =3000.112P h =60,v =3000.539vP p =60,P h =40−0.911P p =90,whereas the injection speed had the large negative corre-lation (r :under −0.9).It means that the injection speed is the most effective of those conditions.3.2.DiscussionIn this section,we discuss the effects of each molding condition,the cavity pressure and the injection speed,separately.First,we focus on that the strong joining was obtained under high pressure conditions.This relationship between the pressure and the strength has been pointed out by the similar study [17],though the study has subjected micro -structures.The difference from the previous study was that the size of surface structures of the metal pieces was nanometer scale;size of each pore was approximately 20nm (see Fig.2).During the molding,the melted plastic flows into the nano-structures of the metal surface to replicate the structures.We assumed that the replication ratio can be higher under the higher pressure conditions (assumption 1).Next,we discuss the effect of the variation of the injection speed by comparison with the previous studies dealing with the IMDJ pro-cess.In the study [15],the authors have reported that the injection speed has no significant effect on the strength;nevertheless we can see a small positive correlation from their data.In addition,the other paper [17]has shown that the injection speed has a large positive correlation with the strength.These results are completely opposite to our result that shows a strong negative correlation between the speed and the strength.Since the melted plastic behaves as liquid,the plastic has viscous resistance while flowing in the cavity.In the case of high viscous resistance,it is difficult for the melted plastic to deform and flow into the surface structures.In consideration of a simple damping model,the viscous resistance is proportional to speed and viscosity.Therefore,the replication ratio of plastic and the resultant strength would be low under high injection speed condition.This viscous resistance effect can occur in not only our case but also the case of the previous studies [15,17].The major difference between our study and others is the size of the surface structures.The metal used in this study had nanometer scale structures,whereas the previous studies used micrometer scale.We assumed that the effect of the viscous resistance should be dominant when the size of surface structures is smaller than a certain size (assumption 2).In this study,we proposed two assumptions about the effects of the cavity pressure and the injection speed.The assumption for the effect of the injection speed was especially unique in the case that the surface structures of the metal piece were nanometer scale.One of our future approaches to confirm the assumptions is to inves-tigate replication ratio by cross-sectional observations/analyses of joining boundaries of the samples processed under various conditions.208 F.Kimura et al./Precision Engineering45(2016)203–2084.ConclusionThis paper presented the metal-plastic direct joining by two basic processes:a surface treatment forming nano-structures and an insert injection molding.We experimentally investigated effects of molding conditions on the joining strength.Here,we summarize thefindings of this study as listed below:•The joining strength had positive correlations with both cavity pressure conditions:the pack pressure and the holding pressure.•The joining strength had a negative correlation with the injection speed.•The effect of the injection speed was much higher than the one of the cavity pressures.The second is especially quite newfinding that has not been reported in the previous studies.We regarded that this is the unique phenomenon for the IMDJ using nano-structures.Additionally,we proposed assumptions that explain the effects of the molding con-ditions on the joining strength from the viewpoint of replication ratio.The replication ratio would be high under high cavity pres-sure condition and be low under high injection speed because of viscous resistance.For future work,we will confirm the assumptions by obser-vations and analyses of joining boundaries.In addition,we will investigate the effects of other conditions,which are surface treatment conditions as well as other molding conditions.Other combinations of conditions can cause different tendencies of strength variations.AcknowledgementsThis work was supported by JSPS KAKENHI(#15K17946),Futaba Electronics Memorial Foundation,and The Foundation for the Promotion of Industrial Science.A part of the experiments was supported by Yokoi group,the University of Tokyo,Japan. References[1]Arenas JM,Alía C,Narbón JJ,Oca na R,González C.Considerations for theindustrial application of structural adhesive joints in the aluminium-composite material pos B:Eng2013;44(1):417–23.[2]Kabche JP,Caccese V,Berube KA,Bragg R.Experimental characterization ofhybrid composite-to-metal bolted joints underflexural pos B:Eng 2007;38(1):66–78.[3]Grujicic M,Sellappan V,Omar M,Seyr N,Obieglo A,Erdmann M,et al.An overview of the polymer-to-metal direct-adhesion hybrid technolo-gies for load-bearing automotive components.J Mater Process Technol 2008;197(1–3):363–73.[4]Katayama S,Kawahito ser direct joining of metal and plastic.Scr Mater2008;59(12):1247–50.[5]Fortunato A,Cuccolini G,Ascari A,Orazi L,Campana G,Tani G.Hybrid metal-plastic joining by means of laser.Int J Mater Form2010;3(1):1131–4.[6]Holtkamp J,Roesner A,Gillner A.Advances in hybrid laser joining.Int J AdvManuf Technol2010;47(9–12):923–30.[7]Bauernhuber A,Markovits ser assisted joining of metal pins and thin plasticsheets.Phys Proc2012;39:108–16.[8]Tan X,Zhang J,Shan J,Yang S,Ren J.Characteristics and formation mechanismof porosities in CFRP during laser joining of CFRP and pos B:Eng 2015;70:35–43.[9]Amancio-Filho ST,Bueno C,dos Santos JF,Huber N,Hage Jr E.On the feasibility offriction spot joining in magnesium/fiber-reinforced polymer composite hybrid structures.Mater Sci Eng:A2011;528(10–11):3841–8.[10]Liu FC,Liao J,Nakata K.Joining of metal to plastic using friction lap welding.Mater Des2014;54:236–44.[11]Balle F,Wagner G,Eifler D.Ultrasonic metal welding of aluminiumsheets to carbonfibre reinforced thermoplastic composites.Adv Eng Mater 2009;11(1–2):35–9.[12]Sasaki H,Kobayashi I,Sai S,Hirahara H,Oishi Y,Mori K.Adhesion of ABS resinto metals treated with triazine trithiol monosodium aqueous solution.J Adhes Sci Technol1999;13(4):523–39.[13]Kang ZX,Mori K,Oishi Y.Surface modification of magnesium alloys using tri-azine dithiols.Surf Coat Technol2005;195(2–3):162–7.[14]Honkanen M,Hoikkanen M,Vippola M,Vuorinen J,LepistöT.Metal-plasticadhesion in injection-molded hybrids.J Adhes Sci Technol2009;23(13–14): 1747–61.[15]Ramani K,Moriarty B.Thermoplastic bonding to metals via injection moldingfor macro-composite manufacture.Polym Eng Sci1998;38(5):870–7.[16]Lucchetta G,Marinello F,Bariani PF.Aluminum sheet surface roughness corre-lation with adhesion in polymer metal hybrid overmolding.CIRP Ann–Manuf Technol2011;60(1):559–62.[17]Seto M,Asami Y,Itakura M,Tanaka H,Yamabe M.Influence of molding condi-tions on joining strength of injection molded parts joined with metal and resin.J Jpn Soc Polym Process2015;27(2):68–74(in Japanese).[18]Taki K,Nakamura S,Takayama T,Nemoto A,Ito H.Direct joining of a laser-ablated metal surface and polymers by precise injection molding.Microsyst Technol2016;22:31–8.[19]Okumura A,Asami Y.Method of manufacturing composite molded article. Patent App.13/990,927.[20]Fabrin PA,Hoikkanen ME,Vuorinen JE.Adhesion of thermoplastic elas-tomer on surface treated aluminum by injection molding.Polym Eng Sci 2007;47(8):1187–91.[21]Naritomi M,Andoh N.Metal and resin composite and manufacturing method Patent App.12/669,143.[22]Rosato DV,Rosato MG.Injection molding handbook.Springer Science&Busi-ness Media;2012.。

专利名称：METHOD OF ESTIMATING A VELOCITYMAGNITUDE OF A MOVING TARGET IN AHORIZONTAL PLANE AND RADARDETECTION SYSTEM发明人：Stachnik, Mateusz,Cieslar, Dariusz申请号：EP18173846.9申请日：20180523公开号：EP3572839A1公开日：20191127专利内容由知识产权出版社提供专利附图：摘要：The present invention relates to a method of estimating a velocity magnitude ofa moving target in a horizontal plane using radar signals received by a radar detection system, the radar detection system being configured to resolve multiple dominant points of reflection, i.e. to receive a plurality of radar signals from the moving target in a single measurement instance of a single, wherein each of the resolved points of reflection is described by data relating to a range, an azimuth angle and a raw range rate of the points of reflection in said single radar measurement instance. The invention further relates to a radar detection system.申请人：Aptiv Technologies Limited地址：Erin Court Bishop's Court Hill St. Michael BB国籍：BB代理机构：Manitz Finsterwald Patent- und Rechtsanwaltspartnerschaft mbB更多信息请下载全文后查看。

专利名称：A cartridge device for a measuring system for measuring viscoelastic characteristics ofa sample liquid,a corresponding measuringsystem, and a corresponding method发明人：Kessler, Max,Romero-Galeano, JoséJavier,Schubert, Axel申请号：EP08172769.5申请日：20081223公开号：EP2202517A1公开日：20100630专利内容由知识产权出版社提供专利附图：摘要：The present invention is directed to a cartridge device (50) for a measuring system (40) for measuring viscoelastic characteristics of a sample liquid (1), in particular a blood sample, comprising a cartridge body (30) having at least one measurement cavity (20, 20') formed therein and having at least one probe element (22, 22') arranged in said at least one measurement cavity (20, 20') for performing a test on said sample liquid (1); and a cover (31) being attachable on said cartridge body (30); wherein said cover (31) covers at least partially said at least one measurement cavity (20, 20') and forms a retaining element for retaining said probe element (20, 20') in a predetermined position within said at least one measurement cavity (20, 20'). The invention is directed to a measurement system (40) and a method for measuring viscoelastic characteristics of a sample liquid (1).申请人：C A Casyso AG地址：Rieserstrasse 8 4132 Muttenz CH国籍：CH代理机构：Peckmann, Ralf更多信息请下载全文后查看。

专利名称：VENT-TYPE INJECTION CONTROLLING METHOD AND VENT TYPE INJECTIONMOLDER发明人：KAMIYAMA TAKASHI,FUJITA SHIGERU 申请号：JP19449686申请日：19860820公开号：JPS6351117A公开日：19880304专利内容由知识产权出版社提供摘要：PURPOSE:To make it possible to suck off the volatile content and water content in molten resin and the air left in a cavity by a method wherein a screw is retreated in non-rotated state so as to develop empty space around the screw under the condition that vent port and a nozzle are closed after the metering of the resin. CONSTITUTION:When the rotation of a screw 32 is stopped and at the same time the screw is retreated in non-rotated state by a distance larger than 'suck back' at the completion of metering, vacuum is produced in a heating cylinder 31 and molten resin A is stored on a screw 32 side under the state that empty space is left at the tip of the heating cylinder 31 and the volatile content and water content are evaporated and separated from the molten resin. After a molded item is removed from a mold, a movable mold 39 is advanced to close the mold and a B-nozzle is brought into touch with a fixed mold 38 by advancing the heating cylinder 31. Under the state just mentioned above, the interior of the heating cylinder 31 and a cavity 40 are evacuated through a vent port 37. In succession, both the nozzles 33 and 36 are brought into close contact with each other by advancing the heating cylinder 31 in order to start an injection process. Accordingly, resin with high hygroscopicity can bemolded without predrying by using the standard non-vent injection molder and, in addition, vacuum forming can be made possible with an ordinary mold.申请人：TOSHIBA MACH CO LTD更多信息请下载全文后查看。

DESCRIPTIONLinacoustic ® RC insulation is a exible duct liner made from strong glass bers bonded with a thermosetting resin. The airstream surface is protected with JM’s exclusive Reinforced Coating system, which combines our state-of-the-art Permacote ® acrylic coating with a exible glass mat reinforcement to provide a smooth airstream surface.FACTORY-APPLIED EDGE COATINGEdge coating is factory applied to the edges of the liner core, ensuring coverage of the leading edges per NAIMA/SMACNA requirements. Shop fabrication cuts may be coated with SuperSeal ® edge treatment (refer to publication AHS-202).USESLinacoustic RC insulation is speci cally designed for lining sheet metal ducts in air conditioning, heating and ventilating systems, providing superior acoustical and thermal performance.STORAGELinacoustic RC should be kept clean and dry during storage, transport, fabrication, installation, and system operation.GENERAL PROPERTIESOperating temperature (max.) – ASTM C411 250°F (121°C)Air velocity (max.) – ASTM C1071 6,000 fpm (30.5 m/sec)Water repellency – INDA IST 80.6 ≥6Fungi resistance – ASTM C1338 Does not breed or promoteFungi resistance – ASTM G21No growthSTANDARD THICKNESSES AND PACKAGING Thickness Roll Length Roll Widths for All Thicknesses*in mm lineal feet lineal meters in mm ½13100, 150, 20031, 46, 6134 to 72864 to 182912550, 100, 150, 20015, 31, 46, 6134 to 72864 to 18291½3850, 10015, 3134 to 72864 to 1829251501534 to 72864 to 1829376.2501555 to 601422 to 1524*Available in ¼” (6.4 mm) increment.Contact your Regional Sales Of ce for stock items and availability of special sizes.SURFACE BURNING CHARACTERISTICSLinacoustic RC duct liner meets the Surface Burning Characteristics and Limited Combustibility of the following standards:Standard/Test Method • ASTM E84 • UL 723 • NFPA 255• NFPA 90A and 90B • NFPA 259• CAN/ULC S102SPECIFICATION COMPLIANCE• ASTM C1071, Type I • ICC Compliant • California Title 24• MEA #353-93-M• Conforms to ASHRAE 62• SMACNA Application Standards for Duct Liners• NAIMA Fibrous Glass Duct Liner Installation Standard • Canada: CGSB 51-GP-11M and CAN/CGSB 51.11ADVANTAGESImproves Indoor Building Environment. Linacoustic RC duct liner improves indoor environmental quality by helping to control both temperature and sound.Resistant to Dust and Dirt. The tough acrylic polymer Permacote coating helps guard against the incursion of dust or dirt into the substrate, minimizing the potential for biological growth.Will Not Support Microbial Growth. Permacote coating is formulated with an immobilized EPA-registered protective agent to protect the coating from potential growth of fungi and bacteria.Linacoustic RC duct liner meets all requirements for fungi and bacterial resistance. Tests were conducted in accordance with ASTM C1338 and ASTM G21 (fungi testing). Detailed information is available in Johns Manville fact sheet HSE-103FS.Note: As with any type of surface, microbial growth may occur in accumulated duct system dirt, given certain conditions. This risk is minimized with proper design, ltration, maintenance and operation of the HVAC system.Cleanability. If HVAC system cleaning is required, the Reinforced Coatingairstream surface may be cleaned with industry-recognized dry methods. See the North American Insulation Manufacturers Association (NAIMA) “Cleaning Fibrous Glass Insulated Air Duct Systems.”Highly Resistant to Water. The reinforced coating surface provides superior resistance to penetration of incidental water into the ber glass wool core.Maximum Flame Spread Index 25Maximum Smoke Developed Index50HVAC-329 05/04/23 (Replaces 08/29/22)Duct liner is UL Classified for E84Duct Liner UL file: R3711THERMAL PERFORMANCE Thickness R-valueConductance in mm (hr•ft 2•°F)/Btu m 2•°C/W Btu/(hr•ft 2•°F)W/m 2•°C ½ 13 2.2 0.39 0.46 2.611 25 4.2 0.74 0.24 1.361½ 38 6.3 1.11 0.16 0.912 51 8.0 1.41 0.13 0.743 76.212.02.110.080.47R-value and conductance are calculated from the material thermal conductivity tested in accordance with ASTM C518 at 75°F (24°C) mean temperature.SOUND ABSORPTION COEFFICIENTS (TYPE “A” MOUNTING)Thickness Sound Absorption Coef cient at Frequency(Cycles per Second) of in mm 125 250 500 1000 2000 4000NRC ½ 13 0.07 0.20 0.44 0.66 0.84 0.93 0.551 25 0.08 0.31 0.64 0.84 0.97 1.03 0.701½ 38 0.10 0.47 0.85 1.01 1.02 0.99 0.852 51 0.25 0.66 1.00 1.05 1.02 1.01 0.953 76.20.47 0.96 1.17 1.10 1.021.05 1.05Coefficients were tested in accordance with ASTM C423 and ASTM E795.ISO 9001:2015 CERTIFICATIONJohns Manville mechanical insulation products are designed, manufactured and tested in our own facilities, which are certi ed and registered to stringent ISO 9001:2015 (ANSI/ASQC 90) series quality standards. This certi cation, along with regular, independent third-party auditing for compliance, is your assurance that Johns Manville products deliver consistent high quality.INSTALLATIONLinacoustic RC duct liner installation must be performed in accordance with the requirements of the NAIMA Fibrous Glass Duct Liner Standards or SMACNA HVAC Duct Construction Standard. All transverse edges, or any edges exposed to air ow, must be coated with an approved duct liner coating material, such as Johns Manville SuperSeal products.Minimizes Pre-installation Damage. Linacoustic RC duct liner’s Reinforced Coating System is highly resistant to damage that can occur during in-shop handling, fabrication, jobsite shipping and installation.Easy to Fabricate. Linacoustic RC duct liner is lightweight and easy to handle. Clean, even edges can be accurately cut with regular shop tools.DATA SHEETLINACOUSTIC ® RCFIBERGLASS DUCT LINER WITH REINFORCED COATING SYSTEMHVAC-329 05/04/23 (Replaces 08/29/22)GREENGUARD ®have been screened for more than 10,000 volatile organic compounds (VOCs) and meet stringent standardsfor low chemical emissions based on established criteria from key public health agenciesHVAC-329 05/04/23 (Replaces 08/29/22)© 2023 Johns Manville. All Rights Reserved.North American Sales Offices, Insulation Systems Eastern Region & Canada P .O. Box 158De ance, OH 43512 800-334-2399 Fax: 419-784-7866Western Region & Outside North America P .O. Box 5108 Denver, CO 80217 800-368-4431 Fax: 303-978-4661Technical speci cations as shown in this literature are intended to be used as general guidelines only. Please refer to the Safety Data Sheet and product label prior to using this product. The physical and chemical properties of Linacoustic RC listed herein represent typical, average values obtained in accordance with accepted test methods and are subject to normal manufacturing variations. They are supplied as a technical service and are subject to change without notice. Any references to numerical ame spread or smoke developed ratings are not intended to re ect hazards presented by these or any other materials under actual re conditions.All Johns Manville products are sold subject to Johns Manville’s standard Terms and Conditions, which includes a Limited Warranty and Limitation of Remedy. For a copy of the Johns Manville standard Terms and Conditions or for information on other Johns Manville thermal insulation and systems, visit /terms-conditions or call (800) 654-3103.717 17th St.Denver, CO 80202 800-654-3103 DUCT LINER INSTALLATIONWhen velocity exceeds 4000 fpm (20.3 m/sec), use metal nosing on Duct Section (Typically 4' or 5' [1.22 m or 1.52 m])ThicknessLINER FASTENERS Liner adhered to the duct with 90% minimum area coverage of adhesive. Adhesive shall conform to ASTM C 916.Shop or eld cuts shall be liberally coated with SuperSeal Edge Treatment or approved adhesive.DATA SHEETLINACOUSTIC ® RCFIBERGLASS DUCT LINER WITH REINFORCED COATING SYSTEMMaximum spacing for fasteners. Actual intervals are approximate.Dimensions A Velocity* in mm in 0–2500 fpm 3 76 12 (0–12.7 m/sec)2501–6000 fpm 3766(12.7–30.5 m/sec)*Unless a lower level is set by the listing agency.DD。