PROXIMITY SENSOR AND METHOD FOR MEASURING THE DISTANCE FROM A TARGET

Abstract

A proximity sensor for measuring the distance from a target contains a microwave oscillator providing a transmission wave output signal emitted toward the target as a free space transmission wave which is reflected by an electrically conductive target surface as a free space reflection wave received by the proximity sensor as a reflection wave. The distance is determined from the transmission wave and the reflection wave. The transmission wave is guided in a waveguide transmission path as a waveguide transmission wave. The transmission wave is coupled into the waveguide with a wave mode leading to the detachment of the waveguide transmission wave at the waveguide front end aperture into the free space transmission wave and to the propagation of the free space transmission wave to the target. At least one reception path is electromagnetically decoupled from the transmission path and guides the reflection wave as a waveguide reflection wave.

Claims

1. Proximity sensor for measuring the distance (D) of a target (12), having a microwave oscillator (52) that provides, as an output signal (54), a transmission wave (16) which is emitted by the proximity sensor (10) in the direction of the target (12) as a free-space transmission wave (16c) that the target (12), which is electrically conductive or at least has an electrically conductive surface, reflects as a free-space reflection wave (30a) and the proximity sensor (10) receives as a reflection wave (30), wherein determining the distance (D) from the transmission wave (16) and the reflection wave (30) is provided, wherein the transmission wave (16) is guided in a waveguide (22) as a waveguide transmission wave (16b), and wherein coupling the transmission wave (16) into the waveguide (22) is provided by a wave mode that leads to detaching the waveguide transmission wave (16b) at the aperture (26) on the front end of the waveguide (22) into the free-space transmission wave (16c) and to propagating the free-space transmission wave (16c) to the target (12), wherein, in the waveguide (22), a transmission path (80) is provided for guiding the transmission wave (16) as a waveguide transmission wave (16b) and at least one receiving path (82) that is electromagnetically decoupled from the transmission path (80) is provided for guiding the reflection wave (30) as a waveguide reflection wave (30b, 30d).

2. Proximity sensor according to claim 1, wherein the waveguide (22) has two separate waveguides for the transmission path (80) and the at least one receiving path (82).

3. Proximity sensor according to claim 1, wherein the two paths (80, 82) that have been decoupled from each other are implemented by a circularly polarized waveguide transmission wave (16b) and a waveguide reflection wave (30b) that is circularly polarized in the other rotational direction, wherein the rotation of the polarization direction on the target (12) takes place by reflection.

4. Proximity sensor according to claim 3, wherein a wave mode transformer (20) is provided to provide the circularly polarized waveguide transmission wave (16b) and to receive the waveguide transmission wave (30b), said wave mode transformer (20) being implemented as a septum polarizer.

5. Proximity sensor according to claim 1, wherein the TE11 mode is provided as the wave mode when using a circular-cylindrical waveguide (22).

6. Proximity sensor according to claim 1, wherein the waveguide (22) is formed to be circular cylindrical.

7. Proximity sensor according to claim 1, wherein a dielectric window (28) is provided at the aperture (26) on the front end of the waveguide (22).

8. Proximity sensor according to claim 1, wherein the waveguide (22) is filled with a dielectric material.

9. Proximity sensor according to claim 1, wherein at least one wave mode transformer (20) is provided in the waveguide (22) for establishing the wave mode of the waveguide transmission wave (16b).

10. Proximity sensor according to claim 1, wherein a quadrature mixer (58) is provided to determine the reflection factor (Γ) from the transmission wave (16) and the reflection wave (30).

11. Proximity sensor according to claim 1, wherein the 6-gate technique is provided to determine the reflection factor (Γ) from the transmission wave (16) and the reflection wave (30).

12. Proximity sensor according to claim 1, wherein the waveguide (22), the wave mode transformer (20) and a signal processing arrangement (14) form a one-part unit, the housing of which is preferably the waveguide (22).

13. Method for measuring the distance (D) of a target (12) in which an output signal (54) of a microwave oscillator (52) is provided as a transmission wave (16) which is emitted in the direction of the target (12) as a free-space transmission wave (16c) that the target (12), which is electrically conductive or at least has an electrically conductive surface, reflects as a free-space reflection wave (30a) and is received as a reflection wave (30), wherein the distance (D) from the transmission wave (16) and the reflection wave (30) is determined, wherein the transmission wave (16) is guided in a waveguide (22) as a waveguide transmission wave (16b), and wherein coupling the transmission wave (16) into the waveguide (22) takes place with a wave mode that leads to detaching the waveguide transmission wave (16b) at the aperture (26) on the front end of the waveguide (22) into the free-space transmission wave (16c) and to propagating the free-space transmission wave (16c) to the target (12), wherein, in the waveguide (22), the transmission wave (16) is led in a transmission path (80) as a waveguide transmission wave (16b) and in at least one receiving path (82) that is electromagnetically decoupled from the transmission path (80) the reflection wave (30) is led as a waveguide reflection wave (30b).

14. Method according to claim 13, wherein the distance (D) is determined from the reflection factor (Γ) or the transmission factor (tr).

15. Method according to claim 13, wherein the distance (D) is determined from the reflection factor (Γ) and the transmission factor (tr).

16. Proximity sensor according to claim 13, wherein the TE11 wave mode is provided as the wave mode when using a circular-cylindrical waveguide (22).

17. Method according to claim 13, wherein the determination of the distance (D) takes place at a frequency of the transmission wave (16) and a wave mode.

18. Method according to claim 13, wherein to determine the distance (D) an adjusting of the microwave oscillator (52) takes place alternatingly on at least two different frequencies of the transmission wave (16) and the determination of the distance (D) takes place on at least two different frequencies and one wave mode.

19. Method according to claim 13, wherein at least one second wave mode is provided for coupling the transmission wave (16) into the waveguide (22) alternatingly to the first wave mode.

20. Method according to claim 19, wherein the determination of the distance (D) takes place at one frequency of the transmission wave (16) and in at least at two different wave modes.

21. Method according to claim 20, wherein such a further wave mode is predetermined that leads to an extensively evanescent field distribution in front of the waveguide (22).

22. Method according to claim 21, wherein the TM01 mode is provided as at least one further wave mode when using a circular-cylindrical waveguide (22).

23. Method according to claim 18, wherein the determination of the distance (D) takes place on at least two different types and a plausibility check of the results determined on different types is provided.

24. Method according to claim 13, wherein a reverse calculation of a determined first reflection factor (Γ) from the transmission wave (16) and the reflection wave (30) is provided on a reflection factor (Γ3) emerging on an aperture (26) of the waveguide (22).

25. Method according to claim 24, wherein the reverse calculation takes place by means of a conformal mapping (38).

26. Method according to claim 24, wherein a determination of the phase (Ph Γ) of the reflection factor (Γ) is provided as a measure for the distance (D).

27. Method according to claim 24, wherein a determination of the phase (Ph Γ) and the amount |Π of the reflection factor (Γ) is provided as a measure for the distance (D).

28. Method according to claim 27, wherein an unambiguous determination of the distance (D) from the phase (Ph Γ) of the reflection factor (Γ) is provided by means of the magnitude of the reflection, factor (Γ) when there is ambiguity of the phase (Ph Γ) of the reflection factor (Γ) within the predetermined measuring region.

29. Method according to claim 13, wherein a rough calibration takes place.

30. Method according to claim 13, wherein a fine calibration takes place.

31. Method according to claim 13, wherein the distance (D) is provided as an analogous signal.

32. Method according to claim 13, wherein a switch signal is provided that signals that a certain distance (D) has been exceeded or has not been reached.

Description

BRIEF DESCRIPTION OF THE FIGURES

[0068] FIG. 1 shows a sketch of a proximity sensor according to the invention,

[0069] FIG. 2a shows a diagram of the electric field strength in a cross section of a waveguide with a first excitation,

[0070] FIG. 2b schematically shows a resulting field strength distribution in the waveguide and in the free space with an excitation according to FIG. 2a,

[0071] FIG. 3a shows a diagram of the electric field strength in a cross section of a waveguide with a second excitation,

[0072] FIG. 3b schematically shows a resulting field strength distribution in the waveguide and in the free space with an excitation according to FIG. 3a,

[0073] FIG. 4a shows a block wiring diagram of a signal processing system,

[0074] FIG. 4b shows a block wiring diagram of a quadrature mixer,

[0075] FIG. 4c shows a block wiring diagram of a 6-gate technique,

[0076] FIG. 5a shows a magnitude of a measured complex reflection factor,

[0077] FIG. 5b shows a phase angle of a measured complex reflection factor,

[0078] FIG. 6a shows a magnitude of a measured complex reflection factor after a conformal mapping,

[0079] FIG. 6b shows a phase angle of a measured complex reflection factor after a conformal mapping and

[0080] FIG. 7 shows a measured reflection factor in two different frequencies after a conformal mapping.

[0081] FIG. 8 shows signal paths decoupled from one another in a waveguide, wherein a transmission path and at least one receiving path are provided,

[0082] FIG. 9 shows a field distribution in the two paths,

[0083] FIG. 10 shows a waveguide in which the uncoupling of the signal paths takes place by means of the circularly polarised waves,

[0084] FIG. 11 shows a top view on the aperture of the waveguide with an indicated circularly polarised free space transmission wave and with an indicated free space reflection wave circularly polarised in the opposing direction and

[0085] FIG. 12 shows a top view on the target, the distance of which is to be measured, with an indicated free space target transmission wave and an indicated free space reflection wave.

DETAILED DESCRIPTION OF THE EXEMPLARY EMBODIMENTS

[0086] FIG. 1 shows a sketch of a proximity sensor 10 corresponding to the prior art according to the non-pre-published patent application PCT/DE2013/000342 that detects the distance D between the proximity sensor 10 and a target 12. The known arrangement serves as a basis for the following description which, however, similarly characterises the proximity sensor according to the invention. The constructive differences between the known arrangement and proximity sensor according to the invention are exposed in connection with the description of the arrangements shown in FIGS. 8-12.

[0087] A signal processing arrangement 14 provides a transmission wave 16 that is guided in a high frequency wire 18 as a wire transmission wave 16a up to a wave mode transformer 20. The wave mode transformer 20 that transfers the wire-bound dual wire wave mode (QTEM) of the wire transmission wave 16a into a predetermined waveguide wave mode, couples the wire transmission wave 16a into a waveguide 22.

[0088] The waveguide 22 has a predetermined cross section that can be rectangular or circular cylindrical, for example. Where necessary, a circular cylindrical construction is advantageous, wherein an immediate exchange of present inductive proximity sensors with circular cylindrical housings compared to the proximity sensor 10 according to the invention in a simple way becomes possible. In particular, available brackets can be used.

[0089] The excited waveguide transmission wave 16b extends in the waveguide 22, reaches an opening or aperture 26 on the front end of the waveguide 22 and determines the field distribution in the region of the aperture 26.

[0090] The waveguide transmission wave 16b running in the waveguide 22, the wave fronts of which being sketched in FIG. 1, appears at the aperture 26 of the waveguide 22 as an irradiated dominating free space transmission wave 16c by which the wave fronts are also sketched. The aperture 26 of the waveguide 22 corresponds to the active surface of the proximity sensor 10.

[0091] The waveguide 22 can have a dielectric window 28 at its aperture 26 on the front end. The dielectric window 28 prevents the penetration of dirt into the waveguide 22. As the material for the dielectric window 28, dielectric materials can be considered, which have as small as possible transmission loss for the waveguide transmission wave 16b. Suitable materials are Teflon or aluminium oxide, for example. Here, the electric permittivity of the material plays a role as the selection criterion since this value, along with the diameter d, also includes the resulting wave impedances of the waveguide wave modes.

[0092] The wave impedance ZHL.sub.∈r of a waveguide filled with dielectric material emerges from the wave impedance ZHL.sub.∈0 of the unfilled waveguide:

[00001]${\mathrm{ZHL}}_{\mathrm{.Math.}.Math..Math.r}=\frac{{\mathrm{ZHL}}_{\mathrm{.Math.}.Math..Math.0}}{\sqrt{\mathrm{.Math.}.Math..Math.r}}$

[0093] In principle, the values should be set in such a way that the characteristic wave impedance of the propagated mode of the waveguide transmission wave 16b corresponds to the wave impedance of the free space Z.sub.F0=377Ω, in front of the waveguide 22. As a result, it is ensured that a reflection-weak transfer from the waveguide transmission wave 16b to the irradiated free space transmission wave 16c takes place.

[0094] Alternatively or additionally to the embodiment with the dielectric window 28, the waveguide 22, where appropriate including the wave mode transformer 20, can be filled with the dielectric material. This embodiment has proved to be particularly advantageous because, in doing so, the wave mode transformer 20 can be mechanically fixed in the waveguide 22. In FIG. 1, the embodiment is shown wherein the wave mode transformer 20 is positioned, seen from the direction of the transmission wave 16, outside the waveguide 22 for depiction-technical reasons.

[0095] The irradiated free space transmission wave 16c meets the target 12 which is at the determined distance D in front of the aperture 26 of the waveguide 22. The proximity sensor 10 according to the invention determines and provides a measure for the distance D between the aperture 26 of the waveguide 22 and the target 12.

[0096] The target 12, which is either made completely from an electrically conductive material or has at least one surface made of an electrically conductive material, reflects the free space transmission wave 16c running outside the waveguide 22, such that a reflection wave 30 occurs that is present at first in the form of a free space reflection wave 30a from which the wave fronts are sketched in FIG. 1. The free space reflection wave 30 goes through the aperture 26 back into the waveguide 22 in which the reflection wave 30 is present as a waveguide reflection wave 30b, wherein, again, the wave fronts of the waveguide reflection wave 30b are sketched.

[0097] The waveguide reflection wave 30b is transferred in the wave mode transformer 20 into a wire reflection wave 30c and go through into the signal processing arrangement 14 as a reflection wave 30.

[0098] The whole arrangement between the signal processing arrangement 14 and the target 12 can be seen in sections as a high frequency wire that is schematically sketched in the lower partial section of FIG. 1. An input impedance Z.sub.1, Z.sub.2, Z.sub.3 or a reflection factor Γ.sub.1, Γ.sub.2, Γ.sub.3 can be allocated to every section. Ideally, a short circuit is on the electrically conductive surface of the target 12, said short circuit leading to an magnitude of the reflection factor Γ.sub.D of at least approximately 1 and to a phase shift of the phase Ph Γ.sub.D between the free space transmission wave and the free space reflection wave 30a from at least approximately 180°.

[0099] According to one embodiment, a measure for the distance D can be determined by means of measuring the impedance Z.sub.1 or the reflection factor Γ.sub.1 that is present at the aperture of the waveguide 22. Depending on the known frequency of the transmission wave 16, the phase Ph Γ.sub.1 of the reflection factor Γ.sub.1 depicts an initially ambiguous measurement for the distance D.

[0100] In the exemplary embodiment shown, the first impedance Z.sub.1 or the first reflection factor Γ.sub.1 appears at the aperture 26 of the waveguide 22. Furthermore, it is assumed that air is present in the free space, the wave impedance of which being at least approximately 377 Ohm. However, a different medium, for example a dielectric wall, can be provided instead of air, wherein then the wave impedance is correspondingly altered.

[0101] The immediate measuring of the reflection factor Γ at the aperture 26 of the waveguide 22, concretely as a measurement of the first reflection factor Γ.sub.1, would technically be very complex. Preferably, therefore, the third reflection factor Γ.sub.3 is measured at the start of the high frequency wire 18 at the position of the signal processing arrangement 14. The substantial advantage is that measuring can be carried out within the signal processing arrangement 14.

[0102] According to line theory, the whole arrangement between the signal processing arrangement 14 and the target 12 can be depicted as a cascade of different wire sections 32, 34, 36. The wire sections 32, 34, 36 are formed by the free space dependent on the distance D, the waveguide 22 and the high frequency wire 18, ignoring the wave mode transformer 20. Every wire section 32, 34, 36 has a specific wave impedance, an (input) impedance Z.sub.1, Z.sub.2, Z.sub.3 and an (input) reflection factor Γ.sub.1, Γ.sub.2, Γ.sub.3.

[0103] Thus, the reflection factors Γ.sub.1, Γ.sub.2, Γ.sub.3 are each based on the wave impedance of the corresponding section 32, 34, 36. For example, the first reflection factor Γ.sub.1 emerges from the (input) impedance Z.sub.1 that is determined at the aperture 26 of the waveguide 22 looking in the direction of the target 12, and from the wave impedance of the free space.

[0104] If, in the first wire section 32, a planar wave is local assumed from the free space, the phase of the first reflection factor Γ.sub.1 has a sectionally linear functional connection to the distance D. With increasing distance D, a monotonous falling function emerges for the magnitude of the first reflection factor Γ.sub.1.

[0105] The nearest wire section 34 that corresponds to the waveguide 22 transforms the impedance Z.sub.1 into the impedance Z.sub.2.

[0106] The third (input) reflection factor Γ.sub.3 of the wire section 36, of the high frequency wire 18 that, in turn, arises from a transformation from Z.sub.2 is easy to measure.

[0107] By means of a conformal mapping 38, a reflection factor corresponding to Γ.sub.1 that expresses a measure for the distance D can be concluded from the third reflection factor Γ.sub.3 that is determined in the signal processing arrangement 14. The reflection factor Γ is a complex size and is defined as a quotient of the reflection wave 30 and the transmission wave 16 that fit the same gate. The reflection factor Γ.sub.1 can, for example, be determined by means of the following context according to a conformal mapping, wherein Z.sub.ref is a normalising impedance that can be set by a rough calibration described below:

[00002]${\Gamma }_1=\frac{Z_3-Z_{\mathrm{ref}}}{Z_3+Z_{\mathrm{ref}}}$$\mathrm{where}$$Z_{\mathrm{ref}}=a+\mathrm{jb}$

[0108] In order to be able to detect the largest possible distances D, according to an exemplary embodiment, as few as possible evanescent contributions to the free space transmission wave 16c in the region in front of the aperture 26 of the waveguide 22 are to be present, since these quickly subside with increasing distance and already only provide a small contribution to the field distribution in a small distance D. It is therefore provided that the free space transmission wave 16c, at least at times, has a dominating contribution to a planar wave propagating in the direction of the target 12 to determine the distance D.

[0109] The field distribution in the aperture 26 is predetermined by the wave mode distribution in the waveguide 22. Therefore, a wave mode is excited that explicitly extensively leads to a free space transmission wave 16c propagating in the direction of the target 12. The waveguide transmission wave 16b should then transfer into the free space transmission wave 16c with as few reflections as possible at the aperture 26. Additionally, the wave impedance of the waveguide wave mode has to correspond to the wave impedance of the free space as much as possible as well as the field distribution thereof having to correspond to the one planar wave as far as possible. These conditions can, for example, be fulfilled by the base wave mode of a rectangular or circular cylindrical waveguide 22.

[0110] Corresponding to the valid norm for inductive proximity sensors, a circular cylindrical constructive shape is predetermined. With an analogous application of the norm for the proximity sensor 10, this means that the waveguide 22 is preferably implemented as a circular cylindrical waveguide 22 having, preferably, a circular cross-section. Without considering the norm that, strictly speaking, only applies to inductive proximity sensors, a freely selectable different cross-section of the waveguide 22, a rectangular cross-section for example, can, however, also be provided, purely in principle.

[0111] In FIGS. 2a-3b, two different field distributions are depicted as an example of a circular cylindrical waveguide 22. In the two examples, the field distributions emerged from the monomodal excitation in the circular cylindrical waveguide 22.

[0112] FIG. 2a shows an excitation 40 in the TE11 mode belonging to a circular cylindrical waveguide. In FIG. 2a, the electric field strength 40 is sketched in a cross-section of the waveguide 22, the magnitude and direction of which are symbolised by the triangles indicated.

[0113] The corresponding field distribution 42 inside the waveguide 22 and the field distribution 44 in the free space in front of the aperture 26 of the waveguide 22 are depicted in FIG. 2b in a top view. The excitation in the TE11 mode leads predominantly to a desired free space transmission wave 16c propagated in the direction of the target 12. Such a propagating free space transmission wave 16c should provide the proximity sensor 10 at least at times.

[0114] FIG. 3a shows a second excitation in the TM01 mode belonging to a circular cylindrical waveguide. The electric field strength 46 is sketched in FIG. 3a in a cross-section of the waveguide 22, the magnitude and direction of which are symbolised by the triangles indicated.

[0115] The corresponding second field distribution 48 inside the waveguide 22 and the second field distribution 50 in the free space in front of the aperture 26 of the waveguide 22 are depicted in FIG. 3b in a top view. The excitation in the TM01 mode leads to an extensively evanescent field distribution 50 in the free space in front of the aperture 26.

[0116] The determination of the reflection factor Γ, especially the third reflection factor Γ.sub.3 takes place in the signal processing arrangement 14, the block wiring diagram of which is shown in FIG. 4a.

[0117] The parts shown in FIG. 4a that correspond to the parts shown in FIG. 1 are provided with the same reference numbers.

[0118] The signal processing arrangement 14, the components thereof being able to be arranged in the back end of the waveguide 22 to correspond to an advantageous embodiment, contains a microwave oscillator 52, the output signal 54 of which is provided both for a directional coupler 56 and for a quadrature mixer 58. The directional coupler 56 leads the output signal 54 of the microwave oscillator 52 via the high frequency wire 18 further on the wave mode transformer 20. Furthermore, the directional coupler 56 uncouples the reflection wave 30 and further leads a reflection signal 60 corresponding to the reflection wave 30 on the quadrature mixer 58.

[0119] Where necessary, a switch 62 is provided. The switch 62 enables switching from a first frequency of the output signal 54 of the microwave oscillator 52 to at least one further frequency.

[0120] In the directional coupler 56, the transmission wave 16 is separated from the reflection wave 30. The directional coupler 56 can be implemented in planar wire techniques, for example in microstrip technique.

[0121] The reflection factor Γ, especially the third reflection factor Γ.sub.3, can be determined on the basis of the separated waves 16, 30, for example by means of quadrature mixing in the quadrature mixer 58.

[0122] A block wiring diagram of the quadrature mixer 58 is shown in FIG. 4b. The quadrature mixer 58 forms an in-phase and a quadrature component I, Q by mixing the reflection wave 30 with the transmission wave 16. The quadrature mix enables the determination of real and imaginary parts of the complex enveloping of the signal to be analysed, here of the reflection signal 60, based on amplitude and phase of the reference signal, here of the output signal 54.

[0123] An alternative opportunity to determine the reflection factor Γ provides the 6-gate technique. An implementation example of the 6-gate technique is shown in FIG. 4c. The 6-gate technique also provides the in-phase and quadrature components I, Q.

[0124] A further alternative opportunity for determining the reflection factor Γ is possible by way of measuring the standing waviness along wiring sections.

[0125] The two components I, Q are supplied to a calculation unit 64 that, as a result, determines the complex reflection factor Γ, especially the third reflection factor Γ.sub.3, and preferably adopts a calibration and a measurement evaluation described further below.

[0126] The calculating unit 64 preferably further contains the conformal mapping 38 for transforming the complex third reflection factor Γ.sub.3 into the first complex reflection factor Γ.sub.1. An output signal 66 of the calculating unit 64 can be evaluated immediately as a measure for the distance D.

[0127] According to an advantageous embodiment of the proximity sensor 10, the microwave oscillator 52, the wave mode transformer 20, the directional coupler 56, the quadrature mixer 58 and the calculating unit 64 are arranged on a single circuit board that is produced from base material that is capable of high frequency, for example fibreglass reinforced Teflon.

[0128] Following the measuring principle, the conformal mapping 38 is provided that depicts the first reflection factor Γ.sub.1 in the complex plane in a spiral with the reference wave impedance as the central point, corresponding to normalising the wave impedance. Thus, all planar waves in the free space between the aperture 26 and the target 12 are combined in a dominating progressive wave. Since this wave loses power by losses and irradiation, both its propagation constant and its wave impedance are complex, as a result of which a complex reference wave impedance ensues.

[0129] If the reference wave impedance of the first reflection factor Γ.sub.1 corresponds to the wave impedance of an equivalent wire, the first reflection factor Γ.sub.1 of a short-circuited wire in complex plane describes a spiral that is run through with increasing distance from the short-circuit in the direction of inside of the spiral.

[0130] Without considering the further influences of the wave mode transformer 20, the course of the third reflection factor Γ.sub.3 describes a spiral in the complex reflection factor plane as a function of the distance D, the location thereof resulting from the individual transformations. Although, in principle, there is still one spiral course, as a result, a complicated course can emerge for the third complex reflection factor Γ.sub.3 in the usual polar coordinate depiction. To illustrate this, it should simply be assumed that the spiral is entirely in the first quadrant of the Cartesian reflection factor plane. By assuming this, a value range of 0 to π/2 for the angle of the reflection factor Γ.sub.1 in polar coordinates ensues. From the phase course that was previously linearly falling with the increasing distance D, now a curve arises that has sectionally cumulative phase values without phase gaps. Similarly, different maximums and minimums in terms of the reflection factor Γ.sub.3 emerge from the transformations. Finally, the aim of the conformal mapping 38 is to eliminate the influence of the impedance transformations by normalising and thus to shift the central point of the spiral course into the origin of the reflection factor plane.

[0131] In FIG. 5a, the magnitude of the third reflection factor Γ.sub.3 is shown in front of the conformal mapping and, in FIG. 6a, after the conformal mapping.

[0132] In FIG. 5b, the phase Ph Γ.sub.1 of the third reflection factor Γ.sub.3 is shown before the conformal mapping and, in FIG. 6b, after the conformal mapping.

[0133] As can be seen, a monotonously falling function and a linear relationship between the distance D and the phase Ph Γ.sub.3 emerges after the conformal mapping for the magnitude of the third reflection factor Γ.sub.3.

[0134] In FIG. 7, the complex third reflection factor Γ, especially the third reflection factor Γ.sub.3 is shown in a Smith diagram, wherein two curve courses are shown that apply to two different frequencies of the transmission wave 16 between which it can be periodically switched by means of the switch 62.

[0135] The distance D of the target 12 can be immediately concluded from the linear phase course by means of the phase constants of the transmission wave 16. As can be seen in FIG. 7, the correlation between distance D and the phase Ph Γ is not initially clear because of the periodicity of the phase course Ph Γ when the detection region of the proximity sensor 10 exceeds half the wavelength of the transmission wave 16. In order to also be able to implement a clear solution for a greater measuring region of the distance D, additionally the reference course of reflection factor Γ is evaluated and thus the ambiguity of the pure phase evaluation is removed. This evaluation is successfully carried out since the conformal mapping 38 depicts the magnitude of determined first refection factor Γ.sub.1 on a monotonous falling course.

[0136] For realising the sensor concept, according to an advantageous embodiment, at least a rough calibration, however preferably a rough and a fine calibration are provided.

[0137] With the rough calibration for the conformal mapping:

[00003]${\Gamma }_1=\frac{Z_3-Z_{\mathrm{ref}}}{Z_3+Z_{\mathrm{ref}}}$

the necessary normalisation impedance:

Z.sub.ref=a+jb

is determined. As a result of the rough calibration, Γ.sub.1 describes a spiral around the origin of the complex reflection factor plane, whereupon a monotonously falling reflection factor magnitude and an approximately linearly falling phase, as shown in FIGS. 6a and 6b, appear. Although the phase runs in a manner that looks to be linear, small deviations from this ideal course are almost unavoidable. The aim of the preferably additionally provided fine calibration is, on the one hand, to approach these deviations through a polynomial that subsequently provides the measuring evaluation for failure compensation. On the other hand, during the fine calibration, a polynomial description of |Γ.sub.1(D)| is developed, by means of which the ambiguity of the phase measuring is removed.

[0138] The basis of the two calibrations form values (reference values) of the complex reflection factor Γ.sub.3 that is received and stored once after producing sensor along the detection region D. The number of value pairs to be obtained is thus mainly determined by the exactness of the sensor that is to be achieved.

[0139] The rough calibration can, for example, be carried out in the following manner:

[0140] In order to be able to take all parasitic influences along the wire sections 36, 34, 32 into account, it is not attempted to analytically determine the normalisation impedance from the equivalent circuit diagram, but to obtain Z.sub.ref directly from the reference values of the finished sensor. Starting with:

Z.sub.ref=a+jb,

the conformal mapping is

[00004]${\Gamma }_1=\frac{Z_3-a-\mathrm{jb}}{Z_3+a+\mathrm{jb}}$

wherein a and b are determined in such a way by an iterative process that |Γ.sub.1| falls monotonously with increasing distance D.

[0141] To do so, |Γ.sub.1(D)| is considered as a function of D with the two parameters a and b. The demand for monotony is of equal important as the disappearance of the local maximum of |Γ.sub.1(D)|. The k position D.sub.i≠0, from which this function attains its maximum, can be found by means of:

[00005]$\frac{d.Math..Math.{\Gamma }_1\left(D_i\right).Math.}{\mathrm{dD}}=0$

and the condition:

[00006]$\frac{d^2.Math..Math.{\Gamma }_1\left(D_i\right).Math.}{d^2.Math.D}<0$

[0142] The aim of the numerical optimisation process is now to determine a and b in such a way that |Γ.sub.1 (D)| becomes minimal and, in an ideal case, k=0 ensues.

[0143] As a starting value of the iteration,

[00007]$Z_{\mathrm{ref}}=\underset{D->\infty }{\lim }.Math.\left(Z_3\right)$

can be provided for selection and thus for calculating |Γ.sub.1|.

[0144] According to one embodiment it is provided to form the wave mode transformer 20 in such a way that this directly performs an impedance transformation of Z.sub.1, whereby the conformal mapping can be greatly simplified or even omitted completely with.

[0145] The preferably additionally provided fine calibration can, for example, be carried out as in the following manner:

[0146] In the first step of the fine calibration, an interpolation polynomial or the function |Γ.sub.1(D)| is developed, the degree of which determines the quality of the approximation. The degree of the polynomial is, in turn, limited by the number of development points, which here are the measured reference points. Since, however, any number of points can be received in a measuring technical manner, an interpolation polynomial can also be found for any exactness. The purpose of this polynomial is to carry out a rough measuring of the distance D by means of the measured reference of the reflection factor F. This measuring serves only to determine the correct interval of the phase.

[0147] The non-linearities that arise in the phase course in practice despite the conformal mapping form directly on the exactness to be expected with the determination of the distance D, To reduce the measuring errors, a linearisation following behind is thus carried out preferably downstream when determining the distance D.

[0148] Based on the phase course of the reflection factor Γ after the conformal mapping, the inconstant phase course is transferred into a constant and clear function by means of |Γ|. The phase values at the individual reference positions are determined by the sensor evaluation and determines the difference between the real value and the desired value. All deviations of the phase along the detection region are again depicted by a polynomial. Here, an arbitrarily high degree and thus an arbitrary exactness can be achieved by an arbitrary number of measuring points.

[0149] If the polynomial is determined and stored, as a result, with the actual determination of distance D, the deviation of the exact phase can be determined and the measuring result can be corrected.

[0150] At this point, it is once again pointed out that the data necessary for the calibration of the proximity sensor 10 according to the invention is determined and stored in a storage that is not shown in more detail in FIG. 4. The proximity sensor 10 provides a measure for absolute distances D and does not need any reference in operation.

[0151] According to a development of the proximity sensor 10 or the method for measuring the distance D of a target 12, it is provided to determine the reflection factor Γ and thus the distance D instead of with a predetermined frequency of the microwave oscillator 54 with at least two different frequencies. To switch between the frequencies, the switch 62 is provided that causes the microwave oscillator 52 to alternatingly provide the output signal 54 with the first and with the at least one further frequency. In doing so, as previously mentioned in connection with FIG. 7, further spiral courses 68, 70 emerge with a correct conformal mapping 38 of the reflection factor Γ for further frequencies. Thus, theoretically, an increasing phase difference Ph Γ ensues from the evaluation at two different frequencies with increasing distance D of the target 12, from said phase difference the clarity can be obtained. This embodiment is particularly advantageous for great distances D since here the course of the reference of the reflection factor Γ is flatter and thus the determination thereof, where necessary, becomes more prone to error.

[0152] In principle, by measuring the distance D with two different frequencies and with one single wave mode, a plausibility check or verification of the determined distance D is possible.

[0153] A further advantageous development provides that, instead of the monomodal excitation, additionally further wave modes are produced in the waveguide 22 and the reflection factor Γ is determined in the different wave modes. As a result, at least one further independent complex size is obtained that can be used for determining the distance D and/or removing the ambiguity in the phase Ph Γ. In this development, several wave mode transformers 20 are required.

[0154] In doing so, a plausibility check or verification of the determined distance D is also possible.

[0155] If necessary, for determining the distance D, both at least two different frequencies of the transmission wave 18 and at least two different wave modes can be used.

[0156] The determined measure for the distance D corresponding to the output signal 66 can be provided as an analogue signal. Alternatively or additionally, the output signal 66 can be provided as a switch signal that signalises that a certain distance D has been exceeded or has not been reached.

[0157] The arrangement previously described and the process previously described for determining the distance D apply not only to the known proximity sensor, but in particular apply in the same way to the proximity sensor 10 according to the invention.

[0158] The proximity sensor 10 according to the invention deviates from the proximity sensor known from the published patent application PCT/DE2013/000342 in that, according to the invention, two paths electromagnetically decoupled from each other in the waveguide 22, a transmission path 80 for the waveguide transmission wave 16b and at least one receiving path 82 for the waveguide reflection wave 30b, are provided.

[0159] The waveguide transmission wave 16b is guided exclusively in the transmission path 80 and irradiated at the aperture 26. The free space transmission wave 16c is reflected on the target 12 and irradiated by the target 12 as the free space reflection wave 30a in the direction of the waveguide 22.

[0160] The free space reflection wave 30a propagates in the receiving path 82 of the waveguide 22. In the exemplary embodiment shown it is assumed that the free space reflection wave 30a propagates not only in the one receiving path 82 but also in the transmission path 80 that thus is the transmission path 80 and receiving path 82 at the same time. Thus, the whole aperture 26 of the waveguide 22 is available for receiving the free space reflection wave 30a.

[0161] In this embodiment, the wave mode transformer 20 is formed in such a way that, on the on hand, it transforms the wire transmission wave 16a into the waveguide transmission wave 16b and transfers the reflected wave 16a in the transmission path 80 again into a wire-bound wave and, on the other hand, converts the hollow reflection wave 30b occurring in the receiving path 82 into a wire-bound wave at the receiving gate. The wave mode transformer 20 is implemented in the shown exemplary embodiment as a septum polariser, the mode of operation thereof having already been extensively described.

[0162] Thus, the reflection factor Γ between the received and transmitted wave in the transmission path 80 and the transmission factor tr between the received weave in the receiving path 82 and the transmitted wave in the transmission path 82 and the transmitted wave in the transmission path 80 can be determined from the wire-bound waves. Thus, the reflection factor Γ is defined by the quotient from the reflected and transmitted wave at one gate and the transmission factor tr is defined by the quotient from the received and transmitted wave at two different gates.

[0163] The substantial advantage with implementing the transmission path 80 and the receiving path 82 electromagnetically decoupled from one another in the waveguide 22 is that, in addition to the reflection factor Γ or alternatively to the reflection factor Γ, the transmission factor tr can be determined.

[0164] With the exemplary embodiment shown in FIG. 8, the uncoupling takes place between the transmission path 80 and the receiving path 82 by two separate waveguides in the waveguide 22 that can be provided by an electrically conductive separating wall 84.

[0165] Assuming that the waveguide 22 is implemented as a cylindrical waveguide 22, FIG. 9 shows a field distribution of the waveguide transmission wave 16b in the transmission path 80 and the waveguide reflection wave 30b in the receiving path 82.

[0166] FIG. 10 shows an advantageous embodiment of the waveguide 22 for implementing the transmission path 80 and the receiving path 82 electromagnetically separated from the transmission path 80. In this embodiment, the whole volume of the waveguide 22 is available for both the waveguide transmission wave 16b and the waveguide reflection wave 30b. Both the waveguide transmission wave 16b and the waveguide reflection wave 30b can use the whole opening provided by the waveguide 22. The separation in the transmission path 80 and the receiving path 82 takes place in the region of the wave mode transformer 20 implemented as a septum polariser, wherein the path 80, 82 are formed on the two sides of the septum polariser. Thus, the whole aperture 26 of the waveguide 22 is available for each signal path 80, 82 such that the irradiating and receiving properties of the waveguide 22 are optimised at a given outer diameter.

[0167] FIG. 11 shows a top view A-A′ on the aperture 26 of the waveguide 22, based on the line A-A′ in FIG. 10. In the exemplary embodiment shown, it is assumed that the waveguide transmission wave 16b is polarised to be circular rotating to the right (viewing direction in the wave propagation direction from behind onto the wave) and is irradiated as a corresponding right-rotating circularly polarised free space transmission wave 16c.

[0168] FIG. 12 shows a top view on the target 12, based on the line B-B′ in FIG. 10. Because of the electrically conductive surface of the target 12, the right-rotating circularly polarised free space transmission wave 16c is reflected as a left-rotating circularly polarised free space wave 30a. Because of the mirror-inverted depicted top view in FIG. 12, based on FIG. 11, the rotational directions of the waves are indicated in opposition.

[0169] The left-rotating circularly polarised free space reflection wave 30a further appears in the waveguide 22 as a left-rotating circularly polarised waveguide reflection wave 30b.

[0170] The wave mode transformer 22 is implemented in the embodiment having circularly polarised waves, preferably as a septum polariser. In the exemplary embodiment shown, the wave mode transformer implemented as a septum polariser has a stepped planar structure that is preferably made with a photolithographic process and can thus be integrated directly on a board including further electronic components. The integration of electronic components in the waveguide 22 has already been explained above in more detail.

[0171] As previously mentioned, the substantial advantage of the invention is in the implementation of electromagnetically decoupled signal paths 80, 82 and that, additionally or alternatively to the reflection factor Γ, the transmission factor tr can be detected that is a measure that is able to be measured and depends on the distance D to the target 12.

[0172] The transmission factor tr describes the signal path that is formed by the transmission path 80 in the waveguide 22, the path course to the target 12 and back again to the receiving path 82 in the waveguide 22.

[0173] The connection between the distance D and the magnitude of the transmission factor tr can be influenced by the shaping of wave guidance inside the waveguide 22. For example, the location of the maximum magnitude is influenced by whether the transmission and receiving track 80, 82 are only led together on the active surface of the proximity sensor 10 or still inside the circular cylindrical waveguide 22. If the two paths 80, 82 run separately from each other up to the active surface, the transmission factor tr is zero at the target distance zero.

[0174] By contrast, the waveguide or sensor head can also be formed in such a way that the magnitude maximum of the transmission factor tr occurs when the target distance is zero, as is possible, for example, when using a septum polariser and circularly polarised waves.

[0175] Thus, in particular, the waveguide 22 can by implemented in such a way that the course of the transmission factor tr qualitatively corresponds to that of the reflection factor F.

[0176] This case brings the considerable advantage that the determination of the distance D can exclusively be based on the determination of the transmission factor tr. In doing so, a signal separation by the directional coupler 56 is not necessary since both the transmission wave 16 and the reflection wave are already separately present.